Laser scanning system mounted over a conveyor belt along which packages bearing bar code symbols are transported and scanned

ABSTRACT

An over-the-conveyor bar code symbol reading system for scanning bar coded packages transported through a 3-D scanning volume having a plurality of focal planes. The system comprises a conveyor belt, first and second laser scanning subsystems mounted thereabove, and a scan data processor. The first laser scanning subsystem generates a first laser scanning pattern above the conveyor belt for scanning each bar coded package transported therealong, and produces bar code position data indicative of the position of the bar code symbol on each scanned package. The second laser scanning subsystem generates and scans a second laser beam to produce a second laser scanning pattern within a 3-D scanning volume above the conveyor belt and having a plurality of focal planes. In response to scanning the transported package, the second laser scanning subsystem produces scan data indicative of the scanned bar code symbol thereon. This scan data is processed to detect each scanned bar code symbol and determine within which one of the plurality of focal planes the detected bar code symbol resides on the transported package. During operation of the system, produced bar code position data is used to automatically set the focal length of the first laser beam to spatially coincide with the focal plane within which the detected bar code symbol resides on the transported package. By virtue of the present invention, bar coded packages of varying height can now be read using a system having reduced complexity and greater compactness for mounting above space-restricted conveyor belts.

RELATED CASES

This is a Continuation of U.S. application Ser. No. 08/886,806 filed Apr. 22, 1997 now U.S. Pat. No. 5,984,185; which is a Continuation of U.S. application Ser. No. 08/726,522 filed Oct. 7, 1996 now U.S. Pat. No. 6,073,846; which is a Continuation of U.S. application Ser. No. 08/573,949 filed Dec. 18, 1995 now abandoned; which is a Continuation-in-Part of U.S. application Ser. No. 08/615,054 filed Mar. 12, 1996 now U.S. Pat. No. 6,286,760; U.S. Ser. No. 08/476,069 filed Jun. 7, 1995 now U.S. Pat. No. 5,591,953; U.S. Ser. No. 08/561,479 filed Nov. 20, 1995 now U.S. Pat. No. 5,661,892 which is a continuation of Ser. No. 08/293,695 filed Aug. 19, 1994 now U.S. Pat. No. 5,468,951; U.S. Ser. No. 08/293,493 filed Aug. 19, 1994 now U.S. Pat. No. 5,525,789;08/475,376 filed Jun. 7, 1995 now U.S. Pat. No. 5,637,852; U.S. Ser. No. 08/439,224 filed May 11, 1995 now U.S. Pat. No. 5,627,359; and U.S. Ser. No. 08/292,237 filed Aug. 17, 1994 now U.S. Pat. No. 5,808,285, each commonly owned by Assignee, Metrologic Instruments, Inc., of Blackwood, N.J., and is incorporated herein by reference as if fully set forth herein.

BACKGROUND OF THE INVENTION

1. Field of Invention

The present invention relates generally to holographic laser scanners of ultra-compact design capable of reading bar and other types of graphical indicia within a large scanning volume using holographic optical elements and visible laser diodes, and also a method of designing and operating the same for use in diverse applications.

2. Brief Description of the Prior Art

The use of bar code symbols for product and article identification is well known in the art. Presently, various types of bar code symbol scanners have been developed. In general, these bar code symbols readers can be classified into two distinct groups.

The first class of bar code symbol reader simultaneously illuminates all of the bars and spaces of a bar code symbol with light of a specific wavelength(s) in order to capture an image thereof for recognition/decoding purposes. Such scanners are commonly known as CCD scanners because they use CCD image detectors to detect images of the bar code symbols being read.

The second class of bar code symbol reader uses a focused light beam, typically a focused laser beam, to sequentially scan the bars and spaces of a bar code symbol to be read. This type of bar code symbol scanner is commonly called a “flying spot” scanner as the focused laser beam appears as “a spot of light that flies” across the bar code symbol being read. In general, laser bar code symbol scanners are subclassified further by the type of mechanism used to focus and scan the laser beam across bar code symbols.

The majority of laser scanners in use today employ lenses and moving (i.e. rotating or oscillating) mirrors in order to focus and scan laser beams across bar code symbols during code symbol reading operations. Examples of such laser scanners are disclosed in great detail in the Background of Invention of U.S. Pat. No. 5,216,232 to Knowles et al.; U.S. Pat. No. 5,340,973 to Knowles et al.; U.S. Pat. No. 5,340,971 to Rockstein et al.; U.S. Pat. No. 5,424,525 to Rockstein et al., which are incorporated herein by reference.

One type of laser scanner that has enjoyed great popularity in recent years is called the “polygon scanner” in that it employs a rotating polygon whose sides bear light reflective surfaces (e.g. mirrors) for scanning a laser beam over multiple paths through space above the scanning window of the scanner. In polygon-type laser scanners, the angular sweep of the outgoing laser beam and the light collection efficiency of the return laser beam are both directly related to the number and size of light reflective facets on the rotating polygon.

In contrast to laser scanners, which use lenses (i.e. light refractive elements) to shape and focus laser light beams and light reflective surfaces to scan focused laser beams, there exists another subclass of laser scanner which employs a high-speed holographic disc. In general, the holographic disc comprises an array or holographic optical elements (HOEs) called “facets” which function to focus and deflect outgoing laser beams during laser beam scanning operations, as well as focus incoming reflected laser light during light collection/detection operations. Such bar code symbol scanners are typically called holographic laser scanners or readers because holographic optical elements (HOEs) are employed. Examples of prior art holographic scanners are disclosed in U.S. Pat. Nos. 4,415,224; 4,758,058; 4,748,316; 4,591,242; 4,548,463; 5,331,445 and 5,416,505, incorporated herein by reference.

Holographic laser scanners, or readers, have many advantages over laser scanners which employ lenses and mirrors for laser beam focusing and scanning (i.e. deflection) functions.

One of the major advantages of holographic laser scanners over polygon laser scanners is the ability of holographic laser scanners to independently control (i) the angular sweep of the outgoing laser beam and (ii) the light collection efficiency for the returning laser beam.

Holographic laser scanners have other advantages over polygon-type laser scanners. In particular, in holographic laser scanners, light collection efficiency is determined by the size of the light collecting portion of each holographic facet, while the angular sweep of the outgoing laser beam is determined by the angular width of the outgoing beam portion of the holographic facet and the angles of incidence and diffraction of the outgoing laser beam.

While prior art holographic scanning systems have many advantages over mirror-based laser scanning systems, prior art holographic scanners are not without problems.

In the first holographic scanner produced by International Business Machines (IBM), the holographic facets on its holographic disc were simple sectors which did not allow for independent control over light collection and light scanning functions. Consequently, such holographic scanners had faster scanning speeds than were needed for the applications at hand. Subsequent industrial scanners designed by IBM allowed independent control of these functions. However, the holographic discs employed in prior art holographic scanners, e.g. the HOLOSCAN2100™ holographic laser scanner designed and sold by Holoscan, Inc. of San Jose, Calif., fail to (i) maximize the use of available space on the disc for light collection purposes, and (ii) minimize the scan line speed for particular laser scanning patterns. As a result of such design limitations, prior art holographic scanners have required the use of large scanning discs which make inefficient use of the available light collecting surface area thereof. They also are incapable of producing from each holographic facet thereon, detected scan data signals having substantially the same signal level independent of the location in the scanning volume from which the corresponding optical scan data signal is produced. Consequently, this has placed great demands on the electrical signal processing circuitry required to handle the dramatic signal swings associated with such detected return signals.

While U.S. Pat. No. 4,415,224 to Applicant (Dickson) discloses a method of equalizing the light collection efficiency of each facet on the holographic scanning disc, it does not disclose, teach or suggest a method of equalizing the light collection efficiency of each facet on the holographic scanning disc, while utilizing substantially all of the light collecting surface area thereof. Thus, in general, prior art holographic laser scanners have required very large scanner housings in order to accommodate very large scanning discs using only a portion of their available light collection surface area.

In many code symbol reading applications, the volumetric extent of the holographic scanner housing must be sufficiently compact to accommodate the small volume of space provided for physical installation. However, due to limitations of conventional design principles, it has not been possible to build prior art holographic scanners having sufficient compactness required in many applications. Consequently, the huge housings required to enclose the optical apparatus of prior art holographic laser scanners have restricted their use to only a few practical applications where housing size constraints are of little concern.

While highly desirable because of their low power usage and miniature size, solid-state visible laser diodes (VLDs) cannot be used practically in prior art holographic laser scanners because of several problems which arise from inherent properties of conventional VLDs.

The first problem associated with the use of VLDs in holographic laser scanners is that the VLDs do not produce a single spectral line output in the manner of conventional He—Ne laser tubes. Rather, conventional VLDs always produce some background super-luminescence, which is a broad spectrum of radiation of the type produced by conventional light emitting diodes (LEDs). Also, VLDs often operate in more than one oscillation mode and/or exhibit mode hopping, in which the VLD jumps from one mode of oscillation to another. Both of these characteristics of VLDs result in a spreading of the laser beam as it leaves the highly dispersive holographic facet of the holographic disc. This results in an effectively larger “spot” at the focal point of the holographic facet, causing errors in the resolution of the bars and spaces of scanned code symbols and, often, intolerable symbol decoding errors.

The second problem associated with the use of VLDs in a holographic scanner is that the inherent “astigmatic difference” in VLDs results in the production of laser beams exhibiting astigmatism along the horizontal and vertical directions of propagation. This fact results in the outgoing laser beam having a cross-sectional dimension whose size and orientation varies as a function of distance away from the VLD. Thus, at particular points in the scanning field of a holographic scanner using a VLD, the orientation of the laser beam (“flying spot”) will be such that the bars and spaces cannot be resolved for symbol decoding operations.

Holographic scanners suffer from other technical problems as well.

In prior art holographic scanners, the light collection and detection optics are necessarily complicated and require a significant volume of space within the scanner housing. This necessarily causes the height dimension of the scanner housing to be significantly larger than desired in nearly all code symbol reading applications.

When an outgoing laser beam passes through, and is diffracted by, the rotating holographic facets of prior art holographic scanners, “holographically-introduced” astigmatism is inherently imparted to the outgoing laser beam. While the source of this type of astigmatism is different than the source of astigmatism imparted to a laser beam due to the inherent astigmatic difference in VLDs, the effect is substantially the same, namely; the outgoing laser beam has a cross-sectional dimension whose size and orientation varies as a function of distance away from the holographic facet. Thus, at particular points in the scanning field of a holographic scanner, the orientation of the laser beam (i.e. “the flying spot”) will be such that the bars and spaces of a scanned bar code symbol cannot be resolved for symbol decoding operations. Consequently, it has been virtually impossible to design a holographic laser scanner with a three-dimensional scanning volume that is capable of scanning bar code symbols independent of their orientation as they move through the scanning volume.

Because of the methods used to design and construct prior art holographic disks, the size and shape of the light collection area of each facet could not be controlled independent of the angular sweep of the outgoing laser beam. Consequently, this has prevented optimal use of the disk surface area for light collection functions, and thus the performance of prior art holographic scanners has been necessarily compromised.

While the above problems generally define the major areas in which significant improvement is required of prior art holographic laser scanners, there are still other problems which have operated to degrade the performance of such laser scanning systems.

In particular, glare produced by specular reflection of a laser beam scanning a code symbol reduces the detectable contrast of the bars and spaces of the symbol against its background and thus the SNR of the optical scan data signal detected at the photodetectors of the system. While polarization filtering techniques are generally known for addressing such problems in laser scanning systems, it is not known how such techniques might be successfully applied to holographic type laser scanning systems while simultaneously solving the above-described problems.

Thus, there is a great need in the art for an improved holographic laser scanning system and a method of designing and constructing the same, while avoiding the shortcomings and drawbacks of prior art holographic scanners and methodologies.

OBJECTS AND SUMMARY OF THE PRESENT INVENTION

Accordingly, a primary object of the present invention is to provide a holographic laser scanner free of the shortcomings and drawbacks of prior art holographic laser scanning systems and methodologies.

Another object of the present invention is to provide a holographic laser scanner which produces a three-dimensional laser scanning volume that is substantially greater than the volume of the housing of the holographic laser scanner itself, and provides full omni-directional scanning within the laser scanning volume.

A further object of the present invention is to provide such a holographic laser scanner, in which the three-dimensional laser scanning volume has multiple focal planes and a highly confined geometry extending about a projection axis extending from the scanning window of the holographic scanner.

A further object of the present invention is to provide such a holographic laser scanner, in which a plurality of symmetrically arranged laser diodes are used to simultaneously produce a plurality of laser beams which are focused and scanned through the scanning volume by a plurality of volume-transmission type holographic optical elements, each of which is supported upon a centrally located rotating disc and particularly designed to produce a single scanning plane of a particular depth of focus when one of the laser beams passes therethrough during the operation of the holographic laser scanner.

A further object of the present invention is to provide such a holographic laser scanner, in which laser light produced from a particular holographic optical element reflects off a bar code symbol, passes through the same holographic optical element, and is thereafter collimated for light intensity detection.

A further object of the present invention is to provide such a holographic laser scanner, in which a plurality of lasers simultaneously produce a plurality of laser beams which are focused and scanned through the scanning volume by a rotating disc that supports a plurality of holographic facets.

A further object of the present invention is to provide such a holographic laser scanner, in which the scanner housing has an apertured scanning window which allows simultaneously projection of multiple scanning planes, at angles which differ from each other over the duration of each scanning pattern generation cycle.

A further object of the present invention is to provide such a holographic laser scanner, in which the holographic optical elements on the rotating disc maximize the use of the disk space for light collection, while minimizing the laser beam velocity at the focal planes of each of the laser scan patterns, in order to minimize the electronic bandwidth required by the light detection and signal processing circuitry.

A further object of the present invention is to provide a compact holographic laser scanner, in which substantially all of the available light collecting surface area on the scanning disc is utilized and the light collection efficiency of each holographic facet on the holographic scanning disc is substantially equal, thereby allowing the holographic laser scanner to use a holographic scanning disc having the smallest possible disc diameter.

A further object of the present invention is to provide a compact holographic laser scanner, in which the beam steering portion of each holographic facet on the holographic scanning disc is provided with a light diffraction efficiency that is optimized for an incident laser beam having a first polarization state, whereas the light collecting portion of each holographic facet is provided with a light diffraction efficiency that is optimized for reflected laser light having a second polarization state orthogonal to the first polarization state, while light focused onto the photodetectors of the system are passed through polarization filters which transmit collected laser light having the second polarization state and block collected laser light having the first polarization state.

A further object of the present invention is to provide such a holographic laser scanner, in which laser beam astigmatism caused by the inherent astigmatic difference in each visible laser diode is effectively eliminated prior to the passage of the laser beam through the holographic optical elements on the rotating scanning disc.

A further object of the present invention is to provide such a holographic laser scanner, in which the dispersion of the relatively broad spectral output of each visible laser diode by the holographic optical elements on the scanning disc is effectively automatically compensated for as the laser beam propagates from the visible laser diode, through an integrated optics assembly, and through the holographic optical elements on the rotating disc of the holographic laser scanner.

A further object of the present invention is to provide such a holographic laser scanner, in which a conventional visible laser diode is used to produce a laser scanning beam, and a simple and inexpensive arrangement is provided for eliminating or minimizing the effects of the dispersion caused by the holographic disc of the laser scanner.

A further object of the present invention is to provide such a holographic laser scanner, in which the inherent astigmatic difference in each visible laser diode is effectively eliminated prior to the laser beam passing through the holographic optical elements on the rotating disc.

A further object of the present invention is to provide such a holographic laser scanner, in which the laser beam produced from each laser diode is processed by a single, ultra-compact optics module in order to circularize the laser beam produced by the laser diode, eliminate the inherent astigmatic difference therein, as well as compensate for wavelength-dependent variations in the spectral output of each visible laser diode, such as superluminescence, multi-mode lasing, and laser mode hopping, thereby allowing the use of the resulting laser beam in holographic scanning applications demanding large depths of field.

A further object of the present invention is to provide such a holographic laser scanner, in which the focal lengths of the multiple focal regions of the laser scanning volume are strategically selected so as to create an overlap at the ends of the scanning planes in the near and far regions of adjacent focal regions in the scanning volume, making it easier to read a bar code symbol passing therethrough independent of its orientation.

A further object of the present invention is to provide such a holographic laser scanner, in which an independent light collection/detection subsystem is provided for each laser diode employed within the holographic laser scanner.

A further object of the present invention is to provide such a holographic laser scanner, in which the geometrical dimensions of its beam folding mirrors in conjunction with the geometrical dimensions of its holographic disc are the sole determinants of the width and length dimensions of the scanner housing, whereas the geometrical dimensions of its beam folding mirrors and parabolic light collecting mirrors beneath the holographic disc are the sole determinants of the height dimension of the scanner housing.

A further object of the present invention is to provide such a holographic laser scanner, in which an independent signal processing channel is provided for each laser diode and light collection/detection subsystem in order to improve the signal processing speed of the system.

A further object of the present invention is to provide such a holographic laser scanner, in which a plurality of signal processors are used for simultaneously processing the scan data signals produced from each of the photodetectors within the holographic laser scanner.

A further object of the present invention is to provide such a holographic laser scanner, in which each facet on the holographic disc has an indication code which is encoded by the zero-th diffraction order of the outgoing laser beam and detected so as to determine which scanning planes are to be selectively filtered during the symbol decoding operations.

A further object of the present invention is to provide such a holographic laser scanner, in which the zero-th diffractive order of the laser beam which passes directly through the respective holographic optical elements on the rotating disc is used to produce a start/home pulse for use with stitching-type decoding processes carried out within the scanner.

A further object of the present invention is to provide a code symbol reading system in which a holographic laser scanner is used to create a scanning volume within which the presence of a code symbol is detected, and a high speed laser scanner is used to scan the region within which the detected bar code resides, to collect high-resolution scan data for decode processing.

A further object of the present invention is to provide a hand-supportable, hand-mounted and body-wearable scanning device employing a holographic scanning mechanism to create various types of scanning patterns, including 2-D raster patterns, within a 3-D scanning volume.

A further object of the present invention is to provide a novel method of designing such a holographic laser scanner having a housing with a minimum height (i.e. depth) dimension for any given three-dimensional laser scanning pattern confined within a specified scanning volume during bar code symbol reading operations.

A further object of the present invention is to provide a novel method of designing a holographic disk for such a holographic laser scanner, such that both the size and shape of the light collection area of each holographic optical element (i.e. facet) on the rotating disc is controlled independent of the angular sweep of the outgoing laser beam in order to make maximum use of the disk surface area for light collection functions during the laser scanning process.

A further object of the present invention is to provide a novel method of designing a laser beam optics module for use with the holographic scanning disc and laser diode employed in the holographic laser scanner hereof, which functions to circularize the laser beam produced from the laser diode, eliminate the inherent astigmatic difference therein, and compensate for wavelength-dependent variations in the spectral output of the visible laser diode, such as superluminescence, multi-mode lasing, and laser mode hopping.

A further object of the present invention is to provide a novel method of designing a holographic disc for a holographic laser scanner, in which all of the available area on the disk is used for optimizing the light collection efficiency thereof and thus improve the performance of the holographic laser scanner.

A further object of the present invention is to provide such disc design method, in which to determine the sizes and shapes of the holographic facets thereof, a 3-D surface geometry program is used to create a 3-D geometrical model of the components of the holographic laser scanner and its 3-D laser scanning pattern, whereas a spreadsheet modelling program is used to create an analytical model for the holographic laser scanner and its 3-D laser scanning pattern.

A further object of the present invention is to provide such disc design method which employs a spreadsheet-type computer program for creating analytical model of the process of generating a prespecified laser scanning pattern using a prespecified holographic facet support disc and beam folding mirror arrangement, and arriving at an optical set of holographic facet parameters which, for prespecified size holographic facet support disc, minimizes the heightwise, lengthwise and widthwise dimensions of the scanner housing.

These and other objects of the present invention will become apparent hereinafter and in the Claims to Invention.

BRIEF DESCRIPTION OF THE DRAWINGS

In order to more fully understand the Objects of the Present Invention, the following Detailed Description of the Illustrative Embodiments should be read in conjunction with the accompanying Figure Drawings in which:

FIG. 1A is a perspective view of the holographic laser scanning system of the present invention shown installed in a first exemplary application environment;

FIG. 1B is a perspective view of the holographic laser scanning system of the present invention shown installed in a second exemplary application environment;

FIG. 1C is a perspective view of the holographic laser scanning system of the present invention shown installed in a third exemplary application environment;

FIG. 2A is a global perspective view of the holographic scanning system of the illustrative embodiment of the present invention, shown with its housing and the light detector support structure removed from its optical bench in order to reveal the holographic scanning disc, beam folding mirrors, laser beam production modules, analog/digital signal processing boards, and other structures otherwise hidden by the housing and the light detector support structure of the system;

FIG. 2B is limited perspective view of the holographic scanning system of the illustrative embodiment, showing in greater detail the beam folding mirror of the first scanning channel of the system, in relation to its associated laser beam production module, parabolic light collection mirror, photodetector and analog/digital signal processing board, arranged about the centrally rotating holographic scanning disc of the system;

FIG. 2C is a partially cut away elevated side view of the holographic scanning system of the illustrative embodiment, showing in greater detail from about the holographic disc, the laser beam production module, beam folding mirror, parabolic light detection mirror and photodetectors associated with one laser station of the system of the present invention;

FIG. 2D is a partially cut away view of the holographic scanning system of the illustrative embodiment, taken along line 2D—2D of FIG. 2C, showing in greater detail the holographic scanning disc, the arrangement of the beam folding mirror and parabolic light detection mirror associated with an illustrative laser scanning station of the system of the present invention;

FIG. 2E is a perspective view of the holographic scanning system of the illustrative embodiment, showing the scanning window array of the scanner housing of the present invention;

FIG. 3 is a plan view of the holographic scanning disc of the illustrative embodiment of the present invention, showing the boundaries of each i-th holographic optical facet mounted thereon about its axis of rotation, with the assigned facet number imposed thereon for illustrative purposes;

FIGS. 4A, 4B and 4C set forth is a block functional diagram of holographic laser scanning system of the illustrative embodiment of the present invention, showing the major components of the system and their relation to each other;

FIG. 5 is a perspective view of the holographic laser scanning system of the illustrative embodiment of the present invention, schematically illustrating the projection of each P(i,j)-th laser scanning plane at its prespecified focal plane (i.e. zone) within the three-dimensional scanning volume extending about the projection axis of the holographic laser scanner;

FIG. 5A is a schematic diagram showing the time order in which each P(i,j)-th laser scanning plane is cyclically generated as the j-th laser beam passes through the i-th holographic facet on the rotating holographic scanning disc within the scanner housing during laser scanning operations;

FIG. 6A is a schematic diagram showing the overlapping nature of the scanlines produced from different holographic facets, between spatially-adjacent focal planes within the laser scanning volume projected from the holographic laser scanner of the present invention;

FIGS. 6B and 6C are schematic diagrams illustrating the various beam cross-sections of two laser scanning beams having focal lengths in the far portion of the scanning volume, shown at a number of different points along their respective scanline trajectories as well as between their respective adjacent focal planes, showing astigmatic laser beam overlapping within each interfocal plane region of the three-dimensional laser scanning pattern;

FIG. 7 is a flow chart illustrating the major steps involved in the method of designing the holographic disc and laser beam production module(s) of the holographic scanning system of the present invention;

FIG. 8A is a geometrical optics model of the process of producing the P(i,j)-th laser scanning plane (i.e. P(i,j)-th laser scanline) located within the three-dimensional scanning volume of the holographic scanning system hereof, by directing the j-th laser beam through i-th holographic facet supported on the rotating holographic scanning disc thereof;

FIG. 8A1 is a view of the geometrical optics model of FIG. 8A, showing particular parameters in greater detail;

FIG. 8B1 and FIGS. 8B2 and 8B3, collectively, show a table listing the parameters used to represent the geometrical optics model of FIGS. 8A and 8A1;

FIGS. 8C1 and 8C2, collectively, show a table listing the mathematical equations describing structural and functional relationships among particular parameters of the geometrical optics model of FIGS. 8A and 8A1;

FIG. 9 is a schematic diagram of the holographic scanning disc of the illustrative embodiment designed according to the method of the present invention, and indicating the various geometrical parameters used to specify the geometrical characteristics of each i-th holographic facet thereof;

FIG. 10A1 is a geometrical optics model illustrating the path travelled by the light rays associated with an incident laser beam being initially diffracted by a rotating holographic facet towards a bar code symbol, then returning light rays reflected therefrom being diffracted again by the same holographic facet towards a light focusing parabolic mirror, and finally the focused light rays being transmitted through the same holographic facet towards its photodetector without diffraction;

FIGS. 10A2 and 10A3 set forth geometrical optics models of the process of a laser beam propagating through a holographic facet on the rotating holographic scanning disc shown in FIG. 10A1, which are used during the disc design process hereof to compute the normalized total out-and-back light diffraction efficiency of each holographic facet to S and P polarized light when no cross-polarizer is used in the holographic laser scanner;

FIG. 10B sets forth a set of parameters used to represent the geometrical optics model of FIGS. 10A1, 10A2, and 10A3;

FIG. 10B1 sets forth a set of initialized (i.e. assumed) values for various parameters used in the geometrical optics models of FIGS. 10A1, 10A2, and 10A3;

FIG. 10C1 sets forth a set of mathematical expressions describing structural and functional relationships among particular parameters of the geometrical optics model of FIGS. 10A1, 10A2, and 10A3;

FIG. 10C2 sets forth a set of equations defining (1) the light diffraction efficiency of the i-th holographic scanning facet to S-polarized outgoing light rays incident on the holographic scanning disc, (2) the light diffraction efficiency of the i-th holographic scanning facet to P-polarized outgoing light rays incident on the holographic scanning disc, and (3) the total out-and-back light diffraction efficiency of the i-th holographic scanning facet to S-polarized outgoing light rays incident on the holographic disc, each being expressed as a function of the modulation-depth (i.e.modulation-index) within a fixed thickness gelatin;

FIG. 10D sets forth a set of equations used to calculate both Fresnel losses and transmission of P and S polarized light rays passing through the holographic scanning facets, for use in the light diffraction efficiency expression set forth in FIG. 10C2;

FIG. 10E1 sets forth a set of graphs plotting, as a function of the modulation-depth (i.e.modulation-index) within a fixed thickness gelatin, (1) the light diffraction efficiency of the first holographic scanning facet to S-polarized outgoing light rays incident thereto, (2) the light diffraction efficiency of the first holographic scanning facet to P-polarized outgoing light rays incident thereto, and (3) the total out-and-back light diffraction efficiency of the first holographic scanning facet to S-polarized outgoing light rays incident, which are ultimately used to compute the total out-and-back light diffraction efficiency of the first holographic facet relative to the total out-and-back light diffraction efficiency of the sixteenth holographic facet;

FIG. 10E2 sets forth a set of graphs plotting, as a function of the modulation-depth (i.e. modulation-index) with a fixed thickness gelatin, (1) the light diffraction efficiency of the sixteenth holographic scanning facet to S-polarized outgoing light rays incident on the sixteenth holographic facet, (2) the light diffraction efficiency of the sixteenth holographic scanning facet to P-polarized outgoing light rays incident on the sixteenth holographic facet, and (3) the total out-and-back light diffraction efficiency of the sixteenth holographic scanning facet to S-polarized outgoing light rays incident on the sixteenth holographic facet, in order to ultimately compute the total out-and-back light diffraction efficiency of the sixteenth holographic scanning facet relative to the total out-and-back light diffraction efficiency of itself (i.e. the sixteenth holographic scanning facet);

FIG. 10F is a schematic diagram illustrating the path travelled by the light rays associated with an incident laser beam being initially diffracted by a rotating holographic facet towards a bar code symbol, then returning light rays reflected therefrom being diffracted again by the same holographic facet towards the light focusing parabolic mirror, and finally the focused light rays being transmitted through the same holographic scanning facet towards the polarized photodetector without substantial diffraction;

FIGS. 10F1 and 10F2 set forth geometrical optics models of the process of a laser beam propagating through a holographic scanning facet in the rotating scanning disc shown in FIG. 10F, which are used during the disc design process to compute the normalized total out-and-back light diffraction efficiency of each holographic scanning facet in the holographic scanning disc of the present invention, when a cross-polarizer is used in the holographic laser scanner;

FIG. 10G sets forth a set of parameters used to represent the geometrical optics models of FIGS. 10F1 and 10F2;

FIG. 10G1 sets forth a set of initial (i.e. assumed) values for particular parameters used to represent the geometrical optics models of FIGS. 10F1 and 10F2;

FIG. 10H1 sets forth a set of mathematical equations describing structural and functional relationships among particular parameters of the geometrical optics model of FIGS. 10F1 and 10F2;

FIG. 10H2 sets forth a set of equations defining (1) the light diffraction efficiency of the i-th holographic scanning facet of FIG. 10F to S-polarized outgoing light rays incident thereto, (2) the light diffraction efficiency of the i-th holographic scanning facet to P-polarized outgoing light rays incident thereto, and (3) the total out-and-back light diffraction efficiency of the i-th holographic scanning facet to S-polarized outgoing light rays incident thereto, each being expressed as a function of the modulation-depth (i.e. modulation-index) within a fixed thickness gelatin;

FIG. 10H3 sets forth a set of equations used to calculate both Fresnel losses and transmission of P and S polarized light rays passing through the holographic scanning facets on the scanning disc, for use in the light diffraction efficiency expression set forth in FIG. 10H2;

FIG. 10I1 sets forth a set of graphs plotting, as a function of the index modulation-depth (i.e. modulation-index) with a fixed thickness gelatin, (1) the light diffraction efficiency of the first holographic scanning facet to S-polarized outgoing light rays incident thereto, (2) the light diffraction efficiency of the first holographic scanning facet to P-polarized outgoing light rays incident thereto, and (3) the total out-and-back light diffraction efficiency of the first holographic scanning facet to S-polarized outgoing light rays incident thereto, in order to ultimately compute the total out-and-back light diffraction efficiency of the first holographic scanning facet relative to the total out-and-back light diffraction efficiency of the sixteenth holographic scanning facet;

FIG. 10I2 sets forth a set of graphs plotting, as a function of the index modulation-depth (i.e. modulation-index) with a fixed thickness gelatin, (1) the light diffraction efficiency of the sixteenth holographic scanning facet to S-polarized outgoing light rays incident thereto, (2) the light diffraction efficiency of the sixteenth holographic scanning facet to P-polarized outgoing light rays incident thereto, and (3) the total out-and-back light diffraction efficiency of the sixteenth holographic scanning facet to S-polarized outgoing light rays incident thereto, in order to ultimately compute the total out-and-back light diffraction efficiency of the sixteenth holographic scanning facet relative to itself (i.e. H₁₆(Δn)=1);

FIG. 10J is a geometrical optics model illustrating the Lambertian light collecting efficiency of the i-th holographic scanning facet on the scanning disc of the present invention;

FIG. 10K sets forth a description of the parameters associated with the geometrical optics model of FIG. 10J;

FIG. 10L sets forth a table of the initial (i.e. assumed) values for particular parameters associated with the geometrical optics model of FIG. 10J;

FIG. 10L1 sets forth a set of equations describing the relationships among the particular parameters in the geometrical optics model of FIG. 10J;

FIGS. 11A through 11C set forth is a flow chart describing, in detail, the steps of the method used to design the holographic scanning disc hereof according to the first illustrative embodiment of the present invention;

FIG. 12 is graphical plot of the light diffraction efficiency of an exemplary holographic scanning facet of the scanning disc of FIG. 3 to S polarized light incident thereto, as a function of the refractive index modulation Δn_(i) (i.e. E_(S)(Δn_(i))), and the light diffraction efficiency of the inner light-collecting portion of the exemplary holographic scanning facet to P polarized light incident thereto, as a function of modulation index Δn_(i)(i.e. E_(P)(Δn_(i))), clearly showing that such light diffraction efficiencies E_(S)(Δn_(i)) and E_(i)(Δn_(i)) do not have peak values at the same value of modulation index Δn_(i) and thus cannot be optimized using the same modulation index Δn_(i) over the entire surface area of the scanning facet;

FIG. 12A is a schematic diagram of the holographic scanning disc of an alternative embodiment of the present invention hereof, in which the outer beam-steering portion of each holographic scanning facet on the scanning disc has a light diffraction efficiency E_(S) (Δn_(i)) which is optimized for an incident laser beam of a first (e.g. S) polarization state by selection of a first optimal modulation index Δn₁, whereas the inner light-collecting portion of the holographic scanning facet has a light diffraction efficiency E_(P)(Δn_(i)) which is optimized for reflected laser light of a second (i.e. P) polarization state orthogonal to the first polarization state by selection of a second optimal modulation index Δn₂;

FIGS. 12B1 through 12B3 provide a flow chart describing, in detail, the steps of the method used to design the holographic scanning disc shown in FIG. 12A;

FIG. 12C is a mathematical expression for the effective relative light diffraction efficiency for facet No. 1 on the scanning disc of FIG. 12A;

FIG. 13 is a geometrical optics model of a holographic recording system which can be used to construct each holographic scanning facet of the scanning disc of the present invention, using the construction parameters determined from the parameter conversion process illustrated in FIGS. 28A1 through 28D;

FIG. 14 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the first illustrative embodiment of the present invention, showing the scanning window of the scanner housing, the holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, parabolic light collecting mirror, and photodetector;

FIG. 14A is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the first illustrative embodiment of the present invention, showing computer-generated schematic indications of both the outgoing and incoming optical paths traversed by laser light produced and detected during the operation of the system;

FIG. 15 is a plan view of the laser beam production module according to the first illustrative embodiment of the present invention comprising a visible laser diode (VLD), an aspherical collimating lens supported within gimbal-like adjustable mounting assembly, and a prism mounted upon a rotatably adjustable platform, and a beam direction changing mirror and a holographic light diffractive grating supported above the optical bench of module;

FIG. 15A is a plan view of the laser beam production module of FIG. 15, with the holographic light diffractive grating and planar mirror removed from the optical bench thereof;

FIG. 15B is a plan view of the optical bench of the laser beam production module of FIG. 15;

FIG. 15C is a side view of the optical bench of the laser beam production module of FIG. 15;

FIG. 15D1 is a side view of the prism support platform of the laser beam production module of FIG. 15;

FIG. 15D2 is a plan view of the prism support platform of the laser beam production module of FIG. 15;

FIG. 15E1 is a plan view of the VLD/lens mount pivot plate of the laser beam production module of FIG. 15;

FIG. 15E2 is a side view of the VLD/lens mount pivot plate of the laser beam production module of FIG. 15;

FIG. 15F1 is a plan view of the VLD/lens mounting bracket (i.e. yoke) of the laser beam production module of FIG. 15;

FIG. 15F2 is a side view of the VLD/lens mounting bracket of the laser beam production module of FIG. 15;

FIG. 15G1 is a cross-sectional view of the VLD/lens mounting tube of the laser beam production module of FIG. 15;

FIG. 15G2 is an axial view of the VLD/lens mounting tube of the laser beam production module of FIG. 15;

FIG. 15H1 is an axial view of the lens barrel of the laser beam production module of FIG. 15;

FIG. 15H2 is a cross-sectional view of the lens barrel of the laser beam production module of FIG. 15;

FIG. 15I1 is a plan view of the prism of the laser beam production module of FIG. 15;

FIG. 15I2 is a side view of the prism of the laser beam production module of FIG. 15;

FIG. 15J is a plan view of the planar beam folding mirror of the laser beam production module of FIG. 15;

FIG. 15K is a plan view of the holographic light diffractive grating (i.e. plate) of the laser beam production module of FIG. 15;

FIG. 16 is a flow chart illustrating the steps of the method used to design the laser beam production module of the first illustrative embodiment of FIG. 15A, using the module components shown in FIGS. 15B through 15K;

FIG. 17A is a geometrical optics model of a holographic light diffractive grating illuminated with a laser beam produced from a conventional visible laser diode (VLD);

FIG. 17B is a set of parameters used to construct the geometrical optics model of the laser beam being diffracted by the holographic light diffractive grating, as shown in FIG. 17A;

FIG. 17B1 is a set of assumed values for particular parameters used to construct the geometrical optics model of FIG. 17A;

FIG. 17C is a set of equations describing functional relationships among certain of the parameters of the geometrical optics model of FIG. 17A;

FIG. 17D is a graphical plot of the diffraction angle of an outgoing laser beam versus the wavelength of the incident laser beam, showing the strong functional dependence of the outgoing diffraction angle on the wavelength of the incident laser beam;

FIG. 18A is a geometrical optics model of the holographic optical system formed by each holographic scanning facet on the scanning disc and the holographic light diffractive grating in the laser beam producing module of the first illustrative embodiment used to substantially decrease the functional dependence of the wavelength of an incident laser beam upon the diffraction angle of the outgoing laser beam from the scanning disc;

FIG. 18B is a set of parameters used to mathematically represent the geometrical optics model shown in FIG. 18A;

FIG. 18B1 is a set of assumed values for particular parameters in the geometrical optics model of FIG. 18A;

FIG. 18C is a set of equations describing the relationships among particular parameters in the geometrical optics model of FIG. 18A;

FIG. 18D is a graphical plot of diffraction angle of the outgoing laser beam versus the wavelength of the incident laser beam, for diffraction angles about the center portion of the diffraction angle range, showing the substantial independence of the angle of diffraction of the outgoing laser beam on the wavelength of the incident laser beam as a result of the optical arrangement of the present invention;

FIGS. 19A and 19B provide a geometrical optics model for an exemplary holographic scanning facet, showing the various parameters used during both construction and reconstruction processes, and conversion from the reconstruction wavelength to the construction wavelength;

FIGS. 19C, 19D1, 19D2 and 19E are a set of given parameters, a set of equations, and a resultant set of numbers, respectively, that determine the hologram construction parameters at a second construction-laser wavelength given the desired hologram performance parameters at a first scanner-laser wavelength.

FIG. 19F is a geometrical optics model of a system used for constructing the holographic scanning facets using the construction parameters determined using the design process of the present invention;

FIG. 20 is a schematic representation of a laser diode, showing the inherent cause of astigmatic difference in visible laser diodes, attributable to the difference in location of the effective sources of the perpendicular and parallel laser beams emitting from the diode junction;

FIG. 20A is a schematic diagram of the optical system used in the laser beam production module of FIG. 15A, for simultaneously circularizing the laser beam and eliminating astigmatism in the laser beam beyond the beam circularizing prism;

FIGS. 20B1, 20B2 and 20B3 provide a geometrical optics model of the optical system of FIG. 20A;

FIG. 20C is a set of parameters used to represent the geometrical optics model of FIGS. 20B1 through 20B3;

FIG. 20C1 is set of assumed values for parameters in the geometrical optics model of FIGS. 20B1 through 20B3;

FIGS. 20D and 20D1 set forth is a set of equations describing functional relationships among particular parameters in the geometrical optics model of FIGS. 20B1 through 20B3;

FIG. 20E is a graphical plot of the distances of the P and S source images (i.e. L_(S2) and L_(P2)) projected by the aspheric collimating lens in the laser beam production module of FIG. 15A, as a function of the distance from the focal point of the aspheric collimating lens to the S-beam source (i.e. d), showing the value of distance (d) at which the P and S sources images converge and astigmatism is reduced to zero;

FIG. 21A is a schematic diagram of an optical system used in aligning the components of the first optical system in the laser beam production module of the first illustrative embodiment, so that astigmatism beyond the prism is reduced to zero;

FIG. 21B is a flow chart indicating the steps of a procedure used to align the components of the first optical system in the laser beam production module of the first illustrative embodiment, so that a desired beam aspect ratio (i.e. “1” for circular beam cross-section) is achieved and astigmatism in the laser beam beyond the second surface of the prism is reduced to zero;

FIG. 21C is a flow chart for a generalized parameter adjustment technique of the present invention;

FIGS. 21C1, 21C2 and 21C3, taken together, provide a flow chart describing a specific procedure for assembling the components of the laser beam production module of the first illustrative embodiment, and also for configuring the geometrical and optical parameters thereof in accordance with the principles of the present invention; and

FIG. 21D is a elevated cross-sectional view of the first and second optical systems of the laser beam production module of the first illustrative embodiment shown coupled together with their geometrical and optical parameters configured to achieve beam dispersion minimization, beam aspect-ratio control, and astigmatism elimination;

FIG. 22 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the second illustrative embodiment, showing the scanning window of the scanner housing, the holographic scanning disc rotatably supported by the motor, the laser beam production module of the second illustrative embodiment, its associated beam folding mirror, parabolic light collecting mirror, and photodetector;

FIG. 23 is an elevated side view of the laser beam production module of the second illustrative embodiment of the present invention, installed upon the optical bench of the laser scanner of the illustrative embodiment with its first and second optical systems coupled together;

FIG. 23A is a plan view of the laser beam production module of the second illustrative embodiment of the present invention, shown with its beam folding mirror and dual-function holographic light diffractive grating removed from the optical bench of the laser beam production module;

FIG. 24 is a flow chart illustrating the steps involved in designing the laser beam production module of FIG. 23 according to the design method of the present invention;

FIG. 25A is a geometrical optics model of the first optical system (i.e. a holographic scanning facet and holographic light diffraction grating) associated with the laser production module of the second illustrative embodiment;

FIG. 25B is a set of parameters used to represent the geometrical optics model of FIG. 25A;

FIG. 25B1 is a set of assumed values for parameters in the geometrical optics model of FIG. 25A;

FIG. 25C is a set of mathematical expressions describing relationships among particular parameters in the geometrical optics model of FIG. 25A;

FIG. 25D provides two plots showing the relationship between (i) the beam incidence angle θ_(i1D) upon the dual-function diffraction grating and the orientation (i.e. tilt angle ρ) of the diffraction grating relative to the holographic scanning disc which provides zero dispersion and (ii) the beam incidence angle θ_(i1M) upon the diffraction grating and the tilt angle ρ of the diffraction grating relative to the holographic scanning disc which provides a desired beam aspect-ratio, wherein the intersection point of these functional plots proves that zero beam dispersion and a desired beam expansion ratio can be achieved by proper selection of tilt angle ρ;

FIG. 25E is a set of construction parameters for constructing the dual-function HOE of the illustrative embodiment of the present invention;

FIG. 26 is a geometrical optics model of the second optical system of the laser beam production module of the second illustrative embodiment, constructed by the Beam Dispersion Analyzer of the present invention in order to determine the performance of this system;

FIG. 27A is a set of parameters used to represent the geometrical optics model in FIG. 26;

FIG. 27B is a set of assumed values for parameters in the geometrical optics model of FIG. 26;

FIG. 27C is a set of mathematical expressions describing relationships among particular parameters of the geometrical optics model of FIG. 26;

FIG. 27D is a plot showing the relationship that exists between (i) the diffraction angle at the holographic disc of an incident laser beam produced from a visible laser diode and (ii) the wavelength thereof when using the first optical system of FIG. 23 to precondition the laser beam prior to its passage through the holographic disc of the holographic scanning system hereof;

FIG. 27D1 is a table of values associated with the graphical plot of FIG. 27D;

FIGS. 28A1 and 28A2 provide a geometrical optics model of the process of changing construction beam angles for a change in wavelength between construction and reconstruction;

FIG. 28B is a set of parameters used to represent the geometric optics model of FIGS. 28A1 and 28A2 including a set of assumed values for parameters in the geometric optics model thereof;

FIGS. 28C1, 28C2 and 28D set forth a set of given parameters, a set of equations, and a resultant set of numbers, that determine the hologram construction parameters at a second construction-laser wavelength given the desired hologram performance parameters at a first scanner-laser wavelength;

FIG. 29 is a schematic diagram of a holographic recording system for constructing the dual-function diffraction grating, using the construction parameters determined from the parameter conversion process of FIGS. 28B and 28C;

FIGS. 30A, 30A1, and 30A2 and 30A3 provide a geometrical optics model of the second optical system of the laser beam production module of the second illustrative embodiment shown in FIG. 23;

FIG. 30B is a set of parameters used to represent the geometrical optics model of FIG. 30A;

FIG. 30B1 is a set of assumed values for certain fixed parameters used to construct the geometrical optics model of FIG. 30B; and

FIGS. 30C1 and 30C2 set forth is a set of mathematical equations describing relationships among particular parameters of the geometrical optics model of FIG. 30A;

FIG. 30D is a graphical plot of the distances of the P and S source images (i.e. L_(S2) and L_(P2)) projected by the aspheric collimating lens in the laser beam production module of the second illustrative embodiment, and the distance from the focal point of the collimating lens to the S-beam source (i.e. d), showing that there exists a value of distance d at which the P and S source images L_(S2) and L_(P2) converge and astigmatism is reduced to zero;

FIGS. 31A1 and 31A2 provide a schematic diagram of the optical system used in aligning the components of the second optical system in the laser beam production module of the first illustrative embodiment, so that astigmatism beyond the dual-function diffractive grating is reduced to zero;

FIG. 31B is a flow chart indicating the procedural steps used to align the components of the second optical system in the laser beam production module of FIG. 23 so that astigmatism beyond the dual-function HOE is reduced to zero;

FIGS. 31C1 and 31C2 provide a flow chart describing a procedure for assembling the components of the laser beam production module of the second illustrative embodiment and configuring the geometrical and optical parameters thereof in accordance with the principles of the present invention;

FIG. 31D is an elevated side view of the first and second optical systems of the laser beam production module of FIG. 23 shown coupled together and mounted on the optical bench of the holographic scanner hereof;

FIG. 32 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the second illustrative embodiment of the present invention, showing the light detection subsystem of the first illustrative embodiment comprising the holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, parabolic light focusing mirror, and photodetector;

FIGS. 33A, 33B and 33C provide a flow chart describing a method of designing a light collection and detection subsystem for a holographic scanner according to the present invention;

FIG. 34 is a geometrical model of the holographic scanner under design prior to the specification of the parabolic mirror and photodetectors;

FIGS. 35A1 and 35A2 provide a geometrical optics model of the light detection subsystem shown in FIG. 32, which does not use cross-polarizers;

FIG. 35B is a set of parameters used to represent the optics model of FIGS. 35A1 and 35A2;

FIG. 35B1 is a set of assumed values for parameters used in the optics model of FIGS. 35A1 and 35A2;

FIGS. 35C1 and 35C2 set forth a set of mathematical expressions describing relations among particular parameters of the geometrical optics model of FIGS. 35A1 and 35A2;

FIG. 35D1 provides a plot of the normalized “average” light diffraction efficiency of the holographic scanning facet No. 1 on the scanning disc as a function of the amount of angular degrees off Bragg (i.e. δ_(e)), where normalized is with respect to the peak diffraction efficiency of facet No. 1 at the Bragg angle.

FIG. 35D2 provides a plot of the normalized “average” light diffraction efficiency of the 16-th holographic scanning facet on the scanning disc as a function of the amount of angular degrees off Bragg (i.e.δ_(e)) where normalized is with respect the peak diffraction efficiency of facet No. 16 at the Bragg angle.

FIG. 36 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system hereof, showing the light detection subsystem of the second illustrative embodiment comprising the holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, parabolic light focusing mirror, photodetector, and a cross S polarizing filter disposed in front of the photodetector;

FIG. 37A is a set of parameters used to represent the optics model of the subsystem of FIG. 36 in which an S polarizing filter is placed before the photodetector, and the geometrical optics model thereof has a similar structure to the geometrical optics model shown in FIGS. 35A1 and 35A2 for the subsystem not employing cross-polarizers;

FIG. 37A1 is a set of assumed values for parameters used in the optics model of the subsystem of FIG. 36;

FIG. 37B sets forth a set of mathematical expressions describing relations among particular parameters of the geometrical optics model of the subsystem of FIG. 36;

FIG. 37C1 provides a plot of the normalized light diffraction efficiency of holographic scanning facet No. 1 on the scanning disc to S Polarized light, expressed as a function of the amount of angular degrees off Bragg (i.e. δ_(e)), where normalization is with respect of the peak diffraction efficiency of facet No. 1 at the Bragg angle;

FIG. 37C2 provides a plot of the normalized light diffraction efficiency of the 16-th holographic scanning facet on the scanning disc to S polarized light, expressed as a function of the amount of angular degrees off Bragg (i.e. δ_(e)) where normalization is with respect to the peak diffraction efficiency of facet No. 16 at the Bragg angle;

FIG. 38A is a set of parameters used to represent the optics model of the subsystem of FIG. 36, in which a S polarizing filter is placed before the photodetector, and the geometrical optics model thereof has a similar structure to the geometrical optics model shown in FIGS. 35A1 and 35A2 for the subsystem not employing cross-polarizers;

FIG. 38A1 is a set of assumed values for parameters used in the optics model of the subsystem of FIG. 36;

FIGS. 38B1 and 38B2 sets forth a set of mathematical expressions describing relations among particular parameters of the geometrical optics model of the subsystem of FIG. 36, where a S polarizer is used;

FIG. 38C1 provides a plot of the normalized light diffraction efficiency of holographic scanning facet No. 1 on the scanning disc to P Polarized light, expressed as a function of the amount of angular degrees off Bragg (i.e. δ_(e)), where normalization is with respect to the peak diffraction efficiency of facet No. 1 at the Bragg angle;

FIG. 38C2 provides a plot of the normalized light diffraction efficiency of the 16-th holographic scanning facet on the scanning disc to P polarized light, expressed as a function of the amount of angular degrees off Bragg (i.e. δ_(e)) where normalization is with respect to the peak diffraction efficiency of facet No. 16 at the Bragg angle;

FIG. 39 is a ray optics diagram showing the paths of the innermost and outermost light rays collected by a holographic scanning facet on the scanning disc associated with the light detection subsystem of the present invention;

FIG. 40A is a plan view of a 3-D geometrical model of scanning disc within the laser scanner of the present invention, illustrating the first step of the method used to determine the first widthwise boundary of the parabolic light collecting surface patch being designed for use in the light detecting subsystem of the system hereof;

FIG. 40B is a plan view of a 3-D geometrical model of scanning disc within the laser scanner of the present invention, illustrating the second step of the method used to determine the second widthwise boundary of the parabolic light collecting surface patch being designed for use in the light detecting subsystem of the system hereof;

FIG. 41 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the fifth illustrative embodiment of the present invention, showing the scanning window of the scanner housing, the transmission-type volume holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, volume-reflection type holographic light focusing element, and photodetector;

FIG. 42 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the sixth illustrative embodiment of the present invention, showing the transmission-type volume holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, and a single light folding mirror, light focusing optics and photodetector disposed beneath the scanning disc;

FIGS. 43A and 43B provide partially cut-away, side cross-sectional views of one scanning channel of the laser scanning system of the seventh illustrative embodiment of the present invention, showing the transmission-type volume holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, and dual light folding mirrors, light focusing optics and photodetector disposed beneath the scanning disc;

FIG. 44 is a partially cut-away, side cross-sectional view of one scanning channel of the laser scanning system of the eighth illustrative embodiment of the present invention, showing the reflection-type volume holographic scanning disc rotatably supported by the motor, the laser beam production module associated with the illustrated scanning channel, its beam folding mirror, and a volume-transmission type holographic light focusing element and photodetector disposed above the scanning disc;

FIGS. 45A and 45B are perspective schematic views of a code symbol scanning system, in which the holographic laser scanner of the present invention is used to detect the presence of code symbols within its scanning volume, and a high-speed laser scanner with variable focal distance is used to scan the region in which the detected code symbol resides to collect high-resolution scan data for use in decode processing;

FIG. 46 is a perspective view of an automatic, hand-supportable holographic laser scanning device constructed in accordance with the principles of the present invention;

FIG. 47 is a schematic representation of a automatic, hand-supportable holographic scanning device constructed in accordance with the present invention, and which produces a two-dimensional raster-type laser scanning pattern within its 3-D scanning volume; and

FIG. 48 is a schematic representation of an automatic holographic laser scanning engine of the present invention, shown mounted on the back of a user's hand for hands-free scanning applications.

DETAILED DESCRIPTION OF THE ILLUSTRATIVE EMBODIMENTS OF THE PRESENT INVENTION

Referring to the figures in the accompanying Drawings, the various illustrative embodiments of the holographic laser scanner of the present invention will be described in great detail.

In the illustrative embodiments, the apparatus of the present invention is realized in the form of an automatic code symbol reading system having a high-speed holographic laser scanning mechanism as well as a scan data processor for decode processing scan data signals produced thereby. However, for the sake of convenience of expression, the term “holographic laser scanner” shall be used hereinafter to denote the bar code symbol reading system which employs the holographic laser scanning mechanism of the present invention.

THE HOLOGRAPHIC LASER SCANNING SYSTEM EMPLOYING A TRANSMISSION-VOLUME TYPE HOLOGRAPHIC LASER SCANNING DISC

As illustrated in FIGS. 1A, 1B and 1C, the holographic laser scanner of the present invention 1 can be used in a diverse variety of code symbol scanning applications. In FIG. 1A, the holographic laser scanner is installed in a warehouse and is used to read bar code symbols 2 on packages 3 for sorting and routing purposes. In FIG. 1B, the holographic laser scanner is installed above the doorway of a storage warehouse and is used to read bar code symbols on packages being loaded in as well as unloaded from the warehouse, as part of an automated inventory control operation. In FIG. 1C, the holographic laser scanner is shown installed above the doorway of a storage container parked against a loading dock, and is used to read bar code symbols on packages being loaded in or unloaded from the container, also as part of an automated inventory control operation.

In FIGS. 2A, through 2E the holographic scanning system 1 is shown with its compact housing enclosure 4 removed from its base 5 which functions as an optical bench for its various optical and electro-optical components. In the illustrative embodiment, the total height of the scanner housing is 6.96 inches, with width and length dimensions of 12.0 and 13.7 inches, respectively, to provide a total internal housing volume (“scanner volume”) V_(housing) of about 1144 cubic inches with a scanner housing depth of 6.96 inches. As will be describe in greater detail below, the total three-dimensional scanning volume produced by this ultra-compact house is 15043.6 cubic inches with a scanning field depth of 30.0 inches. Importantly, the resolution of the bar code symbol that the scanning pattern of the illustrative embodiment can resolve at any location within the specified three-dimensional laser scanning volume V_(scanning) is on the order of about 0.017 inches minimum element width. In the illustrative embodiment (the figure of merit V_(scanning)/V_(housing)=13.15. As will become apparent hereinafter, using the design principles and methods of the present invention disclosed herein, the figure of merit V_(scanning)/V_(housing) can be maximized under a various range of conditions.

As shown in FIG. 2A, the holographic scanning system of the illustrative embodiment comprises three laser scanning stations 6A, 6B and 6C, symmetrically arranged about a holographic scanning disc 7. As best illustrated in FIGS. 2B and 3, the holographic scanning disc 7 comprises two glass plates 8A and 8B, between which are supported a plurality of specially designed holographic optical elements (HOEs), referred to hereinafter as “holographic scanning facets” or “holographic facets”. In the illustrative embodiments, each holographic facet 9 is realized as a volume transmission-type light diffraction hologram having a slanted fringe structure having variations in spatial frequency to provide a characteristic focal length f_(i). The light diffraction efficiency of such volume light diffraction holograms, as a function of incidence angle A_(i), modulation depth Δn_(i), or recording media losses, is described in great detail in the celebrated paper entitled “Coupled Wave Theory for Thick Hologram Gratings” by Herwig Kogelnik, published in The Bell System Technical Journal (BSTJ), Volume. 8, Number 9, at Pages 2909-2947, in November 1969, incorporated herein by reference in its entirety.

In a conventional manner, the glass support plates 8A and 8B forming part of the holographic scanning disc hereof are mounted to a support hub 10. In turn, the support hub is mounted to the shaft of a high-speed, electric motor 11. The other principal subcomponents of each laser scanning station are a laser beam production module 12A (12B, 12C), a planar beam folding mirror 13A (13B, 13C), a parabolic light focusing element (e.g. mirror or volume reflection hologram) 14A (14B, 14C), a photodetector 15A (15B, 15C) with an optional cross-polarizing filter element 16A (16B, 16C) disposed thereacross, an analog scan data signal processing board 17A (17B, 17C), and a digital scan data signal processing board 18A (18B, 18C). For purposes of simplicity of description, when describing the laser scanning stations of the present invention, reference will be made to station 6A. It is understood, however, the stations 6B and 6C have similar structure and operate in substantially the same manner as Station 6A.

The function of each laser beam production module is to cooperate with the holographic scanning disc and produce from its internal visible laser diode (VLD), a laser beam with desired beam cross-sectional characteristics (e.g. having the beam aspect ratio of an ellipse or circle) and being essentially free of astigmatism and beam-dispersion that is otherwise associated with a laser beam directly transmitted from a VLD through a rotating holographic scanning facet during laser beam scanning operations. When an incident laser beam from the VLD passes through a particular holographic scanning facet on the rotating scanning disc, it is diffracted in a prespecified “outgoing” direction (i.e. at an angle of diffraction B_(i))determined during the holographic disc design process of the present invention. The function of the beam folding mirror associated with each scanning station is to change (i.e. fold) the direction of the outgoing diffracted laser beam from its outgoing direction, into the direction required to generate its corresponding laser scanning plane. Notably, when the produced laser scanning plane is intersected by a planar surface (e.g. bearing a bar code symbol), a linear scanline is projected on the intersected surface, as illustrated in FIG. 5. The angular dimensions of each resulting scanning plane are determined by the Scan Angle, θ_(si), associated with the geometry of the scanning facet and the Scan Angle Multiplication Factor, M_(i), associated therewith, which will be discussed in greater detail hereinafter. When a bar code symbol is scanned by any one of the laser scanning planes, the incident laser light is scattered (according to Lambert's Law for diffuse reflective surfaces). A portion of this laser light is reflected back along the outgoing ray path, off the beam folding mirror and thereafter passes through the same holographic scanning facet that generated the corresponding scanning plan only T_(transit)=2−f_(i)/c seconds before, where c is the speed of light. As the reflected laser light passes through the holographic scanning facet on its return path towards the parabolic mirror beneath the scanning disc, the incoming light rays enter the holographic scanning facet close to the Bragg angle thereof (i.e. B_(i)) and thus (once again) are strongly diffracted towards the parabolic mirror along its optical axis. The parabolic mirror, in turn, focuses these collected light rays and redirects the same through the holographic scanning facet at angles sufficiently far off the Bragg angle (i.e. A_(i)) so that they are transmitted therethrough towards the photodetector with minimal losses due to internal diffraction within the holographic facet. A novel method of designing the light detection subsystem of the present invention will be described in great detail hereinafter for various types of holographic scanning discs and light polarization techniques.

As best shown in FIG. 3, the holographic facets on the holographic scanning disc of the present invention are arranged on the surface thereof in a manner which utilizes substantially all of the light collecting surface area provided between the other radius of the scanning disc, r_(outer), and the inner radius thereof, r_(inner). In the illustrative embodiment, sixteen holographic scanning facets are used in conjunction with the three independent laser beam sources, to provide an omni-directional laser scanning pattern consisting of forty-eight (48) laser scanning planes cyclically generated at a rate in excess of 56 times per second. It is understood, however, this number will vary from embodiment to embodiment of the present invention and thus shall not form a limitation thereof. As will be described in greater detail hereinafter, the geometry of each holographic facet has been designed so that (1) each of the sixteen holographic facets supported thereon has substantially the same (i.e. equal) Lamertian light collecting efficiency, independent of its focal length, and (2) the collective surface area of all of the holographic facets occupies (i.e. uses) all of the available light collecting surface area between the outer radius and inner radius of the scanning disc. The advantage of this aspect of the present invention is that optical-based scan data signals with maximum signal-to-noise (SNR) ratio are produced and collected at the photodetector of each laser scanning station in the system. This, of course, implies higher performance and higher quality scan data signals for signal processing.

As shown in FIG. 3, each holographic facet on the surface of the scanning disc is specified by a set of geometrical parameters, a set of optical parameters, and a set of holographic recording parameters. The geometrical parameters define various physical characteristics of the facet in issue, such as the location of the facet on the disc specified by its preassigned facet number (e.g. i=1, 2, 3, . . . or 16), its light collecting surface Area_(i) (designed to exhibit a high diffraction efficiency to incoming light rays on Bragg), the Angle of the facet θ_(roti,) the adjusted Rotation Angle of the facet θ′_(roti) actual scan angle of the facet θ_(sweepi) (accounting for beam diameter d_(beam) and interfaced gaps d_(gap)), and the surface boundaries SB_(i) occupied by the holographic facet on the scanning disc, which typically will be irregular in shape by virtue of the optimized light collecting surface area of the holographic disc). The optical parameters associated with each holographic facet include the wavelength λ at which the object beam is designed to be reconstructed, the angle of incidence of the holographic facet A_(i), the angle of diffraction thereof B_(i), its scan angle multiplication factor M_(i), the focal length f_(i) of the facet, etc. Unlike the other parameters associated with each facet, the recording parameters define the thickness, T, of the recording medium (e.g. dichromate gelatin) used during the recording of the holographic facet, the average bulk index of refraction of the recording medium, and the modulation depth (i.e. modulation-index) Δn_(i) associated with fringe structure formed in the recording medium. Collectively, these parameters shall be referred to as “construction parameters”, as they are required to construct the holographic facet with which they are associated.

In the scanning system of the present invention, the principal function of each holographic facet is to deflect an incident laser beam along a particular path in 3-D space in order to generate a corresponding scanning plane within the 3-D laser scanning volume produced by the scanning system. Collectively, the complex of laser scanning planes produced by the plurality of holographic facets in cooperation with the three laser beam production moldules, creates the highly confined 3-D scanning pattern within the highly defined scanning volume of the scanning system.

As shown in FIG. 5, the holographic laser scanner of the illustrative embodiment cyclically generates from its ultra compact scanner housing 4, a complex three-dimensional laser scanning pattern consisting of forty-eight laser scanning planes, with four different focal planes. This implies that twelve different laser scanning planes are focused in each of the four different focal planes within the 3-D scanning volume. As shown, each of these focal planes extend substantially parallel to the scanning window of the holographic laser scanner and are located at different distances from the scanning window. Thus when each on of these scanning planes is intersected by a planar object, such as a carton wall-surface, twelve laser scanning lines are projected onto its surface, as best shown in FIG. 5. Greater details of the laser scanning pattern of the present invention will be described hereinbelow.

In FIG. 2B, one of the laser scanning stations in the holographic scanner is shown in greater detail. As illustrated in this figure, the beam folding mirror associated with each laser scanning station, has a substantially planar reflective surface 15 and is tangentially mounted adjacent the holographic scanning disc. In the illustrative embodiment, beam folding mirror 13A is supported in this position relative to the house base (i.e. the optical bench) 5 using support legs 16A and 17A and rear support bracket 18A. The angle of inclination of the (j-th beam folding mirror relative to the normal to the holographic disc, φ, will be specified in greater detail during the description of the scanner design process of the present invention. Notably, in order to minimize the height of the holographic scanner housing designated as “h”, and thus design a truly ultra-compact holographic laser scanner, it is necessary to minimize the height of each j-th beam folding mirror relative to housing base designated as “Y_(j)”. As will be described in great detail hereinafter, the design process of the present invention provides a way in which to determined the minimum height of the beam folding mirrors Y_(j), given a prespecified laser scanning pattern, resolution, and holographic disc size, and thus provides a novel method of designing a compact holographic laser scanner having physical dimensions hitherto unattainable using prior art techniques. While the design method of the present invention is shown herein applied to a compact, transportable holographic laser scanner, it is readily applicable to hand-held hand-supportable as well as body mountable holographic laser scanners.

As shown in FIG. 2B, the laser beam production module associated with each laser scanning station is mounted on the optical bench (i.e. housing base plate 5), immediately beneath its associated beam folding mirror. Depending on which embodiment of the laser beam production module is employed in the construction of the holographic laser scanner, the position of the laser beam production module may be different. However, it is preferred that the geometrical dimensions of its beam folding mirrors in conjunction with the geometrical dimensions of its holographic disc are the sole determinants of the width and length dimensions of the scanner housing, whereas the geometrical dimensions of its beam folding mirrors and parabolic light focusing mirror beneath the holographic scanning disc are the sole determinants of the height dimension of the scanner housing. This implies that when designing a holographic laser scanner according to the method of the present invention, the location of the laser beam production modules, the signal processing boards, the motor for rotating the holographic scanning disc, the photodetectors, the beam folding mirrors, the light detection subsystem, and all components other than the holographic scanning disc, do not impose constraints on the geometrical dimensions of the scanner housing. In short, according to the design and construction principles of the present invention, the above-described holographic scanner components can be mounted on the optical bench within the heightwise, widthwise and lengthwise boundary constraints set solely by the geometrical dimensions of the holographic scanning disc, the beam folding mirrors and the parabolic light collecting mirrors beneath the holographic disc. However, as will be shown during the detailed description of the scanner design method hereof, the geometrical dimensions of the laser scanning pattern within the 3-D scanning volume V_(scanning) are what ultimately determine the heightwise, widthwise and lengthwise boundary constraints necessarily imposed on the geometrical dimensions of the holographic disc, the beam folding mirrors and the parabolic light collecting mirrors beneath the holographic scanning disc. Thus, specifications for the laser scanning pattern to be realized provide fundamental constrains for the holographic scanner design process of the present invention.

As shown in FIGS. 2A through 2D, the three laser production modules 12A, 12B and 12C are mounted on base plate 5, symmetrically about the axis of rotation of the shaft of electric motor 11. During laser scanning operations, these laser beam production modules produce three independent laser beams which are directed through the edge of the holographic disc at an angle of incidence A_(i), which, owing to the symmetry of the laser scanning pattern of the illustrative embodiment, is the same for each laser scanning station (i.e. A_(i)=43.0 degrees for all values of i). The incident laser beams produced from the three laser beam production modules 12A, 12B and 12C extend along the three central reference planes 19A, 19B and 19C, each extending normal to the plane of base plate 5 and arranged 120° apart from its adjacent neighboring central planes, as best illustrated in FIG. 2D. While these central reference planes are not real (i.e. are merely virtual), they will be useful in describing the detailed geometrical structure of each laser scanning station in the holographic laser scanner of the present invention.

As shown in FIG. 2B, the photodetector of each laser scanning station is mounted along its central reference plane, above the holographic disc and opposite its associated beam folding mirror so that it does not block or otherwise interfere with the returning (i.e. incoming) laser light rays reflecting off light reflective surfaces (e.g. product surfaces, bar code symbols, etc) during laser scanning and light collecting operations. In the illustrative embodiment, the three photodetectors 15A, 15B and 15C are supported in their respective positions by a photodetector support frame 20 which is stationarily mounted to the optical bench by way of vertically extending support elements 21A, 21B and 21C. The electrical analog scan data signal produced from each photodetector is processed in a conventional manner by its analog scan data signal processing board which is also supported upon photodetector support frame 20. Notably, the height of the photodetector support board, referenced to the base plate (i.e. optical bench), is chosen to be less than the minimum height that the beam folding mirrors must extend above the holographic disc in order to realize the prespecified laser scanning pattern of the illustrative embodiment. In practice, this height parameter is not selected (i.e. specified) until after the holographic disc has been completely designed according to the design process of the present invention, while satisfying the design constraints imposed on the disc design process. As will be explained in greater detail hereinafter, the use of a spreadsheet-type computer program to analytically model the geometrical structure of both the laser scanning apparatus and the ray optics of the laser beam scanning process, allows the designer to determine the geometrical parameters associated with the holographic scanning facets on the disc which, given the specified maximum height of the beam folding mirrors Y_(j), will produce the prespecified laser scanning pattern (including focal plane resolution) while maximizing the use of the available light collecting area on the holographic scanning disc.

As best shown in FIGS. 2B, 2C, 2D and 14, the parabolic light collecting mirror associated with each laser scanning station is disposed beneath the holographic scanning disc, along the central reference plane associated with the laser scanning station. While certainly not apparent, precise placement of the parabolic light collecting element (e.g. mirror) relative to the holographic facets on the scanning disc is a critical requirement for effective light detection by the photodetector associated with each laser scanning station. Placement of the photodetector at the focal point of the parabolic light focusing mirror alone is not sufficient for optimal light detection in the light detection subsystem of the present invention. Careful analysis must be accorded to the light diffraction efficiency of the holographic facets on the scanning disc and to the polarization state(s) of collected and focused light rays being transmitted therethrough for detection. As will become more apparent hereinafter, the purpose of such light diffraction efficiency analysis ensures the realization of two important conditions, namely: (i) that substantially all of the incoming light rays reflected off an object (e.g. bar code symbol) and passing through the holographic facet (producing the corresponding instant scanning beam) are collected by the parabolic light collecting mirror; and (ii) that all of the light rays collected by the parabolic light collecting mirror are focused through the same holographic facet onto the photodetector associated with the station, with minimal loss associated with light diffraction and refractive scattering within the holographic facet. A detailed procedure will be described hereinafter for designing and installing the parabolic light collecting mirror in order to satisfy the critical operating conditions above.

As shown in FIGS. 2A through 2D, the three digital scan data signal processing boards 18A, 18B and 18C are arranged in such a manner to receive and provide for processing the analog scan data signals produced from analog scan data signal processing boards 17A, 17B an 17C, respectively. As best shown in FIGS. 2A and 2B, each digital scan data signal processing board is mounted vertically between a pair of adjacent beam folding mirrors, close to the tangential edge of the holographic disc, within the scanner volume defined by the geometrical dimensions of the holographic disc and the beam folding mirrors. A central processing board 21 is also mounted upon the base plate for processing signals produced from the digital scan data signal processing boards. A conventional power supply board 22 is also mounted upon the base plate, within one of its extreme corners. The function of the digital scan data signal processing boards, the central processing board, and the power supply board will be described in greater detail in connection with the functional system diagram of FIG. 4. As shown, electrical cables are used to conduct electrical signals from each analog scan data signal processing board to its associated digital scan data signal processing board, and from each digital scan data signal processing board to the central processing board. Regulated power supply voltages are provided to the central signal processing board 21 by way of an electrical harness (not shown), for distribution to the various electrical and electro-optical devices requiring electrical power within the holographic laser scanner. In a conventional manner, electrical power from a standard 120 Volt, 60 HZ, power supply is provided to the power supply board by way of flexible electrical wiring (not shown). Symbol character data produced from the central processing board is transmitted over a serial data transmission cable connected to a serial output (i.e. standard RS232) communications jack 23 installed through a wall in the scanner housing. This data can be transmitted to any host device 24 by way of a serial (or parallel) data communications cable, RF signal transceiver, or other communication mechanism known in the art.

As shown in FIG. 2E, the scanner housing has three symmetrically arranged light transmission apertures 25A, 25B and 25C formed in its top wall surface 26. Each of these light transmission apertures has a substantially planar extent which is substantially parallel to the scanning disc rotatable supported upon the shaft of electric motor 11. In order to seal off the optical components of the scanning system from dust, moisture and the like, a laser scanning window 26, preferably fabricated from a high impact plastic material, is installed over each light transmission aperture using a rubber gasket and conventional mounting techniques. In the illustrative embodiment, each laser scanning window 26 has spectrally-selective light transmission characteristics which, in conjunction with a spectrally-selective filter 27 installed before each photodetector within the housing, forms a narrow-band spectral filtering subsystem that performs two different functions. The first function of the narrow-band spectral filtering subsystem is to transmit only the optical wavelengths in the red region of the visible spectrum in order to impart a reddish color or semi-transparent character to the laser scanning window. This makes the internal optical components less visible and thus remarkably improves the external appearance of the holographic laser scanning system. This feature also makes the holographic laser scanner less intimidating to customers at point-of-sale (POS) stations where it may be used. The second function of the narrow-band spectral filtering subsystem is to transmit to the photodetector for detection, only the narrow band of spectral components comprising the outgoing laser beam produced by the associated laser beam production module. Details regarding this optical filtering subsystem are disclosed in copending application Ser. No. 08/439,224, entitled “Laser Bar Code Symbol Scanner Employing Optical Filtering With Narrow Band-Pass Characteristics and Spatially Separated Optical Filter Elements” filed on May 11, 1995, which is incorporated herein by reference in its entirety.

When using multiple laser beam sources in any holographic laser scanning system, the problem of “cross-talk” among the neighboring light detection subsystems typically arises and must be adequately resolved. The cause of the cross-talk problem is well known. It is due to the fact that the spectral components of one laser beam are detected by a neighboring photodetector. While certainly not apparent, the holographic scanning disc of the present invention has been designed so that light rays produced from one laser beam (e.g. j=1) and reflected off a scanned code symbol anywhere within the laser scanning volume V_(scanning) will fall incident upon the light collecting region of the scanning disc associated with a neighboring light detection subsystem in an off-Bragg condition. Consequently, the signal level of “neighboring” incoming scan data signals are virtually undetectable by each photodetector in the holographic laser scanner of the present invention. The optical characteristics of the scanning facets on the scanning disc which makes this feature possible will be described in greater detail hereinafter during the description of the scanning disc design process hereof.

As best shown in FIG. 3, the holographic scanning disc of the present invention is unlike any other prior art laser scanning disc in two important respects. Firstly, virtually all of the utilizable surface area of the scanning disc, defined between the outer edge of the support hub 10 and the outer edge of the scanning disc, is occupied by the collective surface area of all sixteen holographic scanning facets that have been laid out over this defined region. Secondly, each holographic scanning facet has substantially the same Lamertian light collection efficiency as all other scanning facets. Unlike conventional laser scanning discs, the geometry of each holographic facet on the scanning disc of the present invention is apparently irregular, arbitrary and perhaps even fanciful to the eyes of onlookers. The fact is, however, that this is not the case. As will be described in greater detail hereinafter, the scanning disc design process hereof comprises two major stages: a first, “analytical modelling stage” during which particular optical and geometrical parameters are determined for each holographic facet within a complex set of scanning system constraints; and a second, “holographic facet layout stage”, during which the scanning disc designer lays out each holographic facet on the support disc so the virtually all of the available surface area thereon is utilized by the resulting layout. While the disc design method hereof allows certain geometrical parameters associated with each designed holographic facet to be selected on the basis of discretion and judgement of the disc designer (preferably using a computer-aided (CAD) tool) during the holographic facet layout stage, certain geometrical parameters, however, such as the total surface area of each facet Area_(i), its Scan Sweep Rotation (or Sweep Angle θ′_(rot)) and its inner radius R_(i) are determined during the analytical modelling stage by the geometrical structure (e.g. its scanline length, focal plane, and relative position in the scan pattern) associated with the corresponding laser scanline P (i,j) produced by the holographic facet within a particular focal plan of the prespecified laser scanning pattern. Consequently, particular parameters determined during the analytical modelling stage of the design process operate as constraints upon the disc designer during the facet layout stage of the process. Thus, the holographic facets realized on the scanning disc of the present invention have particular geometrical characteristics that are directly determined by geometrical properties of the laser scanning pattern produced therefrom, as well as the optical properties associated with the laser beam and the holographic facets realized on the scanning disc. This fact, while presently subtle, will become readily apparent during the detailed description of the holographic scanning disc design process of the present invention.

As shown in the system diagram of FIGS. 4A through 4C, the holographic laser scanning system of the present invention comprises a number of system components, many of which are realized on boards that have been hereinbefore described. For sake of simplicity, it will be best to describe these system components by describing the components realized on each of the above-described boards, and thereafter describe the interfaces and interaction therebetween.

In the illustrative embodiment, each analog scan data signal processing board 17A, 17B, 17C has the following components mounted thereon: an associated photodetector 17A (17B, 17C) (e.g. a silicon photocell) for detection of analog scan data signals (as described); an analog signal processing circuit 35A (35B, 35C) for processing detected analog scan data signals; a 0-th diffraction order signal detector 36A (36B, 36C) for detecting the low-level, 0-th diffraction order signal produced from each holographic facet on the rotating scanning disc during scanner operation; and associated signal processing circuitry 37A (37B, 37C) for detecting a prespecified pulse in the optical signal produced by the 0-th diffraction order signal detector and generating a synchronizing signal S(t) containing a periodic pulse pattern. As will be described below in greater detail, the function of the synchronizing signal S(t) is to indicate when a particular holographic facet (e.g. Facet No. i=1) produces its 0-th order optical signal, for purposes of linking detected scan data signals with the particular holographic facets that generated them during the scanning process.

In the illustrative embodiment, each photodetector 17A, 17B and 17C is realized as an opto-electronic device and each analog signal processing circuit 35A (35B, 35C) aboard the analog signal processing board is realized as an Application Specific Integrated Circuit (ASIC) chip. These chips are suitably mounted onto a small printed circuit (PC) board, along with electrical connectors which allow for interfacing with other boards within the scanner housing. With all of its components mounted thereon, each PC board is suitably fastened to the photodetector supported frame 20, along its respective central reference frame, as shown in FIG. 2B.

In a conventional manner, the optical scan data signal D₀ focused onto the photodetector 16A (16B or 16C) during laser scanning operations is produced by light rays of a particular polarization state (e.g. S polarization state) associated with a diffracted laser beam being scanned across a light reflective surface (e.g. the bars and spaces of a bar code symbol) and scattering thereof, whereupon the polarization state distribution of the scattered light rays is typically altered when the scanned surface exhibits diffuse reflective characteristics. Thereafter, a portion of the scattered light rays are reflected along the same outgoing light ray paths toward the holographic facet which produced the scanned laser beam. These reflected light rays are collected by the scanning facet and ultimately focused onto the photodetector of the associated light detection subsystem by its parabolic light reflecting mirror disposed beneath the scanning disc. The function of each photodetector is to detect variations in the amplitude (i.e. intensity) of optical scan data signal D₀, and produce in response thereto an electrical analog scan data signal D₁ which corresponds to such intensity variations. When a photodetector with suitable light sensitivity characteristics is used, the amplitude variations of electrical analog scan data signal D₁ will linearly correspond to light reflection characteristics of the scanned surface (e.g. the scanned bar code symbol). The function of the analog signal processing circuitry is to band-pass filter and preamplify the electrical analog scan data signal D₁ in order to improve the SNR of the output signal.

In the illustrative embodiment, each digital scan data signal processing board 18A (18B and 18C) is constructed the same. On each of these signal processing boards, the following devices are realized. An analog-to-digital (A/D) conversion circuit 38A (38B, 38C) is realized as a first application specific integrated circuit (ASIC) chip. A programmable digitizing circuit 39A (39B, 39C) is realized as a second ASIC chip. Also, a programmed decode computer 40A (40B, 40C) is realized as a microprocessor and associated program and data storage memory and system buses, for carrying out symbol decoding operations. In the illustrative embodiment, the ASIC chips, the microprocessor, its associated memory and systems buses are all mounted on a single printed circuit (PC) board, using suitable electrical connectors, in a manner well known in the art.

The function of the A/D conversion circuit is to perform a simple thresholding function in order to convert the electrical analog scan data signal D₁ into a corresponding digital scan data signal D₂ having first and second (i.e. binary) signal levels which correspond to the bars and spaces of the bar code symbol being scanned. In practice, the digital scan data signal D₂ appears as a pulse-width modulated type signal as the first and second signal levels thereof vary in proportion to the width of bars and spaces in the scanned bar code symbol.

The function of the programmable digitizing circuit is to convert the digital scan data signal D2, associated with each scanned bar code symbol, into a corresponding sequence of digital words (i.e. a sequence of digital count values) D₃. Notably, in the digital word sequence D3, each digital word represents the time length associated with each first or second signal level in the corresponding digital scan data signal D₂. Preferably, these digital count values are in a suitable digital format for use in carrying out various symbol decoding operations which, like the scanning pattern and volume of the present invention, will be determined primarily by the particular scanning application at hand. Reference is made to U.S. Pat. No. 5,343,027 to Knowles, incorporated herein by reference, as it provides technical details regarding the design and construction of microelectronic digitizing circuits suitable for use in the holographic laser scanner of the present invention.

In bar code symbol scanning applications, the function of the programmed decode computer is to receive each digital word sequence D₃ produced from the digitizing circuit, and subject it to one or more bar code symbol decoding algorithms in order to determine which bar code symbol is indicated (i.e. represented) by the digital word sequence D₃, originally derived from corresponding scan data signal D₁ detected by the photodetector associated with the decode computer. In more general scanning applications, the function of the programmed decode computer is to receive each digital word sequence D₃ produced from the digitizing circuit, and subject it to one or more pattern recognition algorithms (e.g. character recognition algorithms) in order to determined which pattern is indicated by the digital word sequence D₃. In bar code symbol reading applications, in which scanned code symbols can be any one of a number of symbologies, a bar code symbol decoding algorithm with auto-discrimination capabilities can be used in a manner known in the art.

As shown in FIGS. 4A through 4C, the central processing board 21 comprises a number of components mounted on a small PC board, namely: a programmed microprocessor 42 with a system bus and associated program and data storage memory, for controlling the system operation of the holographic laser scanner and performing other auxiliary functions; first, second, third and forth serial data channels 43, 44, 45 and 46, for receiving serial data input from the programmable decode computers 40A (40B and 40C) and RF receiver/base unit 47; an input/output (I/O) interface circuit 48 for interfacing with and transmitting symbol character data and other information to host computer system 24 (e.g. central computer, cash register, etc.); and a user-interface circuit 49 for providing drive signals to an audio-transducer 50 and LED-based visual indicators 51 used to signal successful symbol reading operations to users and the like. In the illustrative embodiment, each serial data channel is be realized as an RS232 port, although it is understood that other structures may be used to realize the function performed thereby. The programmed control computer 42 also produces motor control signals, and laser control signals during system operation. These control signals are received as input by a power supply circuit 52 realized on the power supply PC board 22, identified hereinabove. Other input signals to the power supply circuit 52 include a 120 Volt, 60 Hz line voltage signal from a standard power distribution circuit. On the basis of the received input signals, the power supply circuit produces as output, (1) laser source enable signals to drive VLDs 53A, 53B and 53C, respectively, and (2) motor enable signals in order to drive the scanning disc motor 11.

In the illustrative embodiment, RF base unit 47 is realized on a very small PC board 54 mounted on the base plate 5 within the scanner housing. Preferably, RF base unit 47 is constructed according to the teachings of copending U.S. application Ser. No. 08/292,237 filed Aug. 17, 1995, also incorporated herein by reference. The function of the base unit 47 is to receive data-packet modulated carrier signals transmitted from a remotely situated bar code symbol reader, data collection unit, or other device capable of transmitting data packet modulated carrier signals of the type described in said application Ser. No. 08/292,237, supra.

In some holographic scanning applications, where omni-directional scanning cannot be ensured at all regions within a prespecified scanning volume, it may be useful to use scan data produced either (i) from the same laser scanning plane reproduced many times over a very short time duration while the code symbol is being scanned therethrough, or (ii) from several different scanning planes spatially contiguous within a prespecified portion of the scanning volume. In the first instance, if the bar code symbol is moved through a partial region of the scanning volume, a number of partial scan data signal fragments associated with the moved bar code symbol can be acquired by a particular scanning plane (e.g. P(i=1, j=3) being cyclically generated over an ultra-short period of time (e.g. 1-3 milliseconds), thereby providing sufficient scan data to read the bar code symbol. In the second instance, if the bar code symbol is within the scanning volume, a number of partial scan data signal fragments associated with the bar code symbol can be acquired by several different scanning planes being simultaneously generated by the three laser scanning stations of the system hereof, thereby providing sufficient scan data to read the bar code symbol, that is, provided such scan data can be identified and collectively gathered at a particular decode processor for symbol decoding operations.

In order to allow the holographic scanner of the present invention to use symbol decoding algorithms that operate upon partial scan data signal fragments, as described above, the 0-th order signal detector and its associated processing circuitry are used to produce a periodic signal X(t), as discussed briefly above. As the periodic signal X(t) is generated by the 0-th order of the incident laser beam passing through the outer radial portion of each holographic facet on the rotating scanning disc, this signal will include a pulse at the occurrence of each holographic facet interface. However, in order to uniquely identify a particular facet for reference purposes, a “gap”0 of prespecified width d_(gap), as shown in FIG. 3, is formed between two prespecified facets (i.e. i=2 and 16) at the radial distance through which the incident laser beam passes. Thus, in addition to the periodic inter-facet pulses, the periodic signal X(t) also includes a “synchronizing pulse” produced by the prespecified “gap” which is detectable every T=2π/ω [seconds], where ω is the constant angular velocity of the holographic scanning disc maintained by the scanning disc motor and associated driver control circuitry. Thus, while the function of the 0-th order light detector is to detect the 0-th diffractive order of the incident laser beam, the function of its associated signal processing circuitry is to (1) detect the periodic occurrence of the “synchronizing pulse” in the periodic signal X(t) and (2) simultaneously generate a periodic synchronizing signal S(t) containing only the periodic synchronizing pulse stream. The construction of such pulse detection and signal generation circuitry is well known within the ordinary skill of those in the art.

As each synchronizing pulse in the synchronizing signal S(t) is synchronous with the “reference” holographic facet on the scanning disc, the decode processor (i.e. computer) (40A, 40B, 40C) provided with this periodic signal can readily “link up” or relate, on a real-time basis, (1) each analog scan data signal D₁ it receives with (2) the particular holographic facet on the scanning disc that generated the analog scan data signal. To perform such signal-to-facet relating operations, the decode computer is provided with information regarding the order in which the holographic facets are arranged on the scanning disc. Such facet order information can be represented as a sequence of facet numbers (e.g. i=1, 16, 2, 15, 9, 12, 6, 11, 7, 10, 5, 8, 3, 13, 4, 14, 1) stored within the associated memory of each decode processor. By producing both a scan data signal and a synchronizing signal S(t) as described above, the holographic scanner of the present invention can readily carry out a diverse repertoire of symbol decoding processes which use partial scan data signal fragments during the symbol reading process. The advantages of this feature of the system will become apparent hereinafter.

In code symbol reading applications where partial scan data signal fragments are used to decode scanned code symbols, the synchronizing signal S(t) described above can be used to identify a set of digital word sequences D₃, (i.e. {D_(s)}), associated with a set of time-sequentially generated laser scanning beams produced by a particular holographic facet on the scanning disc. In such applications, each set of digital word sequences can be used to decode a partially scanned code symbol and produce symbol character data representative of the scanned code symbol. In code symbol reading applications where complete scan data signals are used to decode scanned code symbols, the synchronizing signal S(t) described above need not be used, as the digital word sequence D₃ corresponding to the completely scanned bar code symbol is sufficient to carry out symbol decoding operations using conventional symbol decoding algorithms known in the art.

DESCRIPTION OF THE 3-D LASER SCANNING PATTERN OF THE ILLUSTRATIVE EMBODIMENT OF THE PRESENT INVENTION

Referring to FIG. 5, the laser scanning pattern generated by the holographic scanner hereof is illustrated in greater detail. For illustrative purposes, the laser scanlines that are projected onto each of the four focal plane of the scanning volume, are shown as black lines labelled with their respective scanline (i.e. scanning plane) designation, P(i,j). Each such scanline has a scanline length which is defined, for the most part, by the geometry of the scanning volume V_(scanning), the boundaries of which are indicated by dotted lines, as shown. While the laser scanning pattern of the illustrative embodiment has forty-eight scanning planes in total, only three scanning planes (i.e. scanlines) are simultaneously generated at any instant in time. However, within a single revolution of the holographic scanning disc, all forty-eight scanning planes are generated. The order in which each scanning plane is produced during a single revolution of the scanning disc is described by the schematic representation shown in FIG. 5A. As indicated in this figure, the laser source and holographic facet used to generate each scanning plane are indicated by its holographic facet number i and laser source number j.

It is appropriate at this juncture to now describe the cross-sectional characteristics of the laser scanning pattern of the present invention, and the advantages provided thereby in omni-directional scanning applications.

While the laser beam production module of the present invention provides a novel way to produce a circularized laser beam free of astigmatism due to intrinsic properties of visible laser diodes (VLD), the laser scanning planes P(i,j) generated by the rotating holographic scanning disc diffracting an astigmatism-free laser beam are not completely free of astigmatism. By virtue of the fact that an incident collimated laser beam is scanned through a light diffractive element at an angle of incident A_(i) other than zero degrees, results in astigmatism within the scanning volume. This form of astigmatism, referred to as “beam-scan astigmatism”, manifests itself at the end of each scanline and at the extreme portions of the depth of field for each set of scanlines.

While not necessarily apparent, there are several reasons why a zero degree angle of incidence (i.e. A_(i)=0) cannot be used to eliminate astigmatism in the holographic scanner of the present invention. The first reason is that this approach would greatly reduce the scan angle multiplication factor M for each scanning facet, thus making it impossible to achieve the scan pattern of the illustrative embodiment. Secondly, this approach would reduce the Total Light Collection Efficiency of the facets, as the angles of diffraction B_(i) would have to be lower to realize the spatially corresponding scanline. Thirdly, this approach would necessarily result in a holographic scanning disc which would be extremely difficult to manufacture.

As shown in FIG. 6A, adjacent scanning planes overlap between focal regions within the scanning volume. Each scanning plane is produced as each holographic facet is rotated through a circularized laser beam directed incident thereto at about A_(i)=47° for all values of i. While each scanning plane is often visualized as a continuous sheet of light, in actuality it is made up of a single laser beam whose movement is progressively advanced while its cross-sectional dimensions are changed as the laser beam is diffracted through its scanline path in space.

Using the ZEMAX optional program from Focus Software, In. of Tucson, Ariz., the spot-diagrams of FIGS. 6B and 6C can be generated in order to analyze the astigmatic characteristics of the scanned laser beams comprising the scanning pattern of the present invention. As shown in FIGS. 6B and 6C, the spot size (i.e. cross-sectional) dimensions and orientation of a particular scanned laser beam are represented at its focal plane for five different distances along one half of the scanning plane, as well as for two planes above its focal plane and for two planes below its focal plane. In reality, the spacing of these scanning planes from the focal plane are −120 mm, −60 mm, 60 mm, 120 mm, respectively. The five different spot-size distances represented along the scanning plane correspond to five different angular rotations of the scanning disc about its axis of rotation. Notably, spot-size diagrams shown in FIG. 6B are for a scanned laser beam having its focal plane located farther out from the scanning window, whereas the spot-size diagrams shown in FIG. 6C are for a scanned laser beam having its focal plane adjacent to the focal plane of FIG. 6B, and closer to the scanning window. The far right side of the spot-size diagram shown in FIGS. 6A and 6B represent the middle of the neighboring scanning planes. The middle set of spot-size diagrams represent the cross-sectional diameter and orientation of the laser beam at its focal plane within the scanning volume. The upper set of spot-size diagrams represent the cross-sectional diameter and orientation of the laser beam above its focal plane within the scanning volume. The lower set of spot-size diagrams represent the cross-sectional diameter and orientation of the laser beam below it focal plane within the scanning volume

In each of the spot-size diagrams shown in FIGS. 6B and 6C, the beam orientations are governed by the astigmatism introduced as the incident laser beam is diffracted by its corresponding holographic facet moving about the disk axis of rotation. At each focal plane in the scanning volume, a particular laser beam is focused thereat with astigmatic characteristic that are opposite those of the neighboring laser beam which spatially overlaps the particular laser beam. As illustrated in FIGS. 6A and 6B, the direction of beam orientation, measured from the middle of the scan line, at the focal plane, rotates in a direction opposite the direction that the neighboring overlappiong laser beam rotates. Consequently, in the region of overlapping laser beams between each adjacent pair of focal planes within the scanning volume, the complementary beam cross-sectional characteristics cooperate to provide an omni-directional scanning field over the extent of the spatially overlapping scanning planes. Thus, when a bar code to be scanned is oriented in a manner which makes it difficult to read the symbol due to the tilt of the astigmatic spot in the near portion of the two adjacent focal regions, the tilt of the astigmatic spot in the adjacent far field region is in the opposite direction, making it easier to read the same code symbol. Collectively, the overlapping scanning planes between adjacent focal regions within the scanning volume provides robust omni-directional code symbol scanning performance.

DESIGNING A HOLOGRAPHIC LASER SCANNING SYSTEM ACCORDING TO THE METHOD OF THE PRESENT INVENTION

In FIG. 7, the four primary steps involved in designing a holographic laser scanner according to the present invention are shown.

As indicated at Block A in FIG. 7, the first step of the design method involves geometrically specifying the following entitles: (i) the structure of the three-dimensional scanning pattern and scanning volume to be realized; (ii) the performance parameters of the scanner to be designed; and (iii) the volumetric dimensions of the scanner housing from which the scanning pattern is to be generated. Typically, each of these entities will be specified by end user requirements which include factors such as: the scanning application and environment at hand; bar code symbol resolution; reflection characteristics of bar code symbol substrate; speed of objects being identified; and the throughput of the scanning environment.

Thus, as part of this specification step, the number and location of each scanning plane (i.e. focal plane), and its focal distance f_(i) within the specified scanning volume must be specified in geometrical terms, that is, using coordinate geometry etc. In general, this step involves providing a geometrical specification of the 3-D laser scanning pattern, as shown in FIGS. 5, 6A, 6B and 6C, for example. In short, this procedure necessitates specifying a coordinate system (e.g. Cartesian coordinate system), and then specifying the location of each scan line (i.e. scanning plane) within the scanning volume and its focal distance f_(i) from the i-th holographic scanning facet. Naturally, the resolution of the bar code symbols to be read will determine the largest cross sectional dimension that each scan line can be in order to resolve the bar code symbol. Thus, it will be necessary to provide a proper specification of the maximum cross-sectional diameter of the scanned laser beams within the operative scanning range of the specified scanning volumes.

As shown in FIG. 3, the scanning pattern of the illustrative embodiments has four specified focal planes, indexed as k=1,2,3,4. Each of the scan lines within each of the focal planes is specified in terms of its geometrical coordinates. For example, four focal planes are used in the illustrative embodiment to satisfy a 40 inch depth of field requirement for the exemplary application at hand. While this may appear conservative at first, it has been found that this four focal plane design offers an important advantage over other system designs in that it provides a vertical “sweet spot” in the central portion of the 3-D scanning volume. In the illustrative embodiment, each of these four focal planes are parallel to the scanning window of the scanner, and each of the four scan patterns in the four focal planes are centered over the rotational axis of the rotating holographic disk. Also, the lines at each focal plane are space equally apart from each other. The basic four line scan pattern selected in the illustrative embodiment provides good coverage of the scan region at each focal plane. From the customer requirements, the minimum and maximum focal distances and lengths of each scanline S_(L) in the scanning volume V_(scanning) can be established (i.e. determined) in order to completely cover each of the scanning regions in the scanning volume.

As indicated at Block B of FIG. 7, the next step of the design method involves selecting a basic architecture for the laser scanning platform upon which the designed scanning pattern will be produced. In the illustrative embodiment shown in FIGS. 1 through 4, the laser scanning apparatus selected as suitable laser scanning platform for the envisioned 3-D scanning pattern, comprises three symmetrical laser scanning stations constructed about the holographic scanning disc of the present invention, each of the laser scanning stations has a laser beam production module and light collecting and detecting subsystem. The three laser scanning station architecture adopted in the illustrative embodiment, provides the best method for generating the bar-X scan pattern of the exemplary scan pattern. The symmetry of the scanning pattern dictates that all three laser scanning channels should be the same, allowing that the design for any one channel be the same as that for the other three channels. For the sake of convenience, the scan pattern created at each of the focal planes should be centered over the rotational axis of the holographic scanning disk, although it is understood that this is not a necessary condition. As will be shown hereinafter, the design method of the present invention allows one to easily change system parameters so that the axially centered scanning pattern can be changed to a non-centered location, or the scan pattern can be configured in a non-symmetrical manner, away from the axis of rotation of the holographic scanning disk.

Having specified the 3-D scanning pattern and platform architecture for a given application, the next step in the scanner design method indicated in FIG. 7 hereof involves using the scanning pattern and volume specifications and scanner housing specifications to design a particular scanning platform comprising a holographic scanning disc of the present invention and an array beam folding mirrors configured in such a manner so the resultant system produces the specified scanning pattern. Preferred disk design methods will be described in great detail below with reference to FIGS. 8A through 12C. Also, a preferred method of constructing the designed scanning disk will be described thereafter with reference to FIG. 13.

As indicated at Block D in FIG. 7, the next step of the method involves designing a laser beam production module using the holographic scanning disk specifications acquired at Block B. Notably, the scanning disk specifications required during this step of the design method include the angle of incidence A_(i) for each facet, the angle of diffraction B_(i) thereof, and the central wavelength λ_(i) of the laser beam produced from the VLD. As will be described in great detail hereinafter, the function of the laser production module is to produce an incident laser beam that has a circularized (or aspect-ratio controlled) beam cross-section, is free from the effects of astigmatism along its operative scanning range, and, which, in conjunction with the laser scanning disk, minimizes dispersion of spectral components thereof as the laser beam is diffractively transmitted through the facets along the rotating scanning disk. In the illustrative embodiments, two different techniques are employed in order to realize the above described functions utilizing ultra-compact structures. In the first illustrative embodiment of the present invention shown in FIGS. 14 through 21D, a VLD, an aspherical lens, a beam expanding prism, a light diffractive grating of fixed spatial frequency are used to construct the laser beam production module of the present invention. In the second illustrative embodiment of the present invention shown in FIGS. 22 through 31D, an aspherical lens, and a multi-function light diffractive grating of fixed spatial frequency are used to construct the laser beam production module hereof. In both embodiments, novel design techniques are employed which, for the first time, allow the use of conventional VLDs in a holographic code symbol reading system without sacrificing high performance characteristics.

As indicated in Block E in FIG. 7, the last step of the design method involves specifying and designing a light collecting and detecting subsystem (hereinafter “light detection subsystem”) for use with the designed holographic laser scanner. As will be described in greater detail hereinafter with reference to FIGS. 32 through 43B, several different types of subsystems may be used to realize this system component in accordance with the principles of the present invention.

In the first preferred embodiment of the light collecting and detecting subsystem, a parabolic mirror is disposed beneath the light collecting area of the scanning disk and is designed to focus incoming collected light rays towards a photodetector disposed at the focal length of the parabolic mirror above the scanning disk. The focal characteristics of the parabolic mirror and its position relative to the scanning disc are chosen so that each focused light ray is transmitted through the scanning disk at an angle of incidence which minimizes the light diffraction efficiency thereof. In the second illustrative embodiment of the light collecting and detecting subsystem, a reflective-volume type holographic diffraction grating of variable spatial frequency is disposed beneath the light collecting area of the scanning disk and is designed to focus incoming collected light rays towards a photodetector disposed at the focal length of the reflection-volume type holographic grating above the scanning disk. The focal characteristics of the parabolic reflection-volume hologram and its position relative to the scanning disc are chosen such that each focused light ray is transmitted through the scanning disk at an angle of incidence which minimizes the light diffraction efficiency thereof. The third illustrative embodiment of the light collecting and detecting subsystem includes a planar mirror, light focusing optics and a photodetector disposed beneath the light collecting area of the scanning disk. Each of these embodiments will be described in detail hereinafter with reference to FIGS. 32 through 43B.

Referring to FIGS. 11A through 11C, the major steps involved in practicing the “holographic scanner” design method hereof will now be described in great detail. Notably, this term is used herein to describe the overall process used to design all of the subsystems of the holographic laser scanner including, but not limited to, the holographic scanning disc, the beam folding mirror array, the light collecting and detecting subsystem, the laser beam production modules, as well as the scanner housing within which such subsystems are contained. Thus, the holographic scanner design method hereof comprises a collection of subsystem design methods and processes which interact with each other to provide a composite method. In general, there are numerous embodiments of the holographic scanner design method of the present invention. Factors which influence the design of the scanning disc and light detection subsystem include, for example, the polarization state of the incident laser beam used during scanning operations, as well as the polarization state of the laser light rays collected, focused and detected by the light collecting and detecting subsystem used during light collecting and detecting operations.

In the illustrative embodiments of the present invention, the scanner design methods hereof are carried out on a computer-aided design (CAD) workstation which can be realized using a computer system, such as the Macintosh 8500/120 computer system. In the illustrative embodiment, the CAD-workstation supports a 3-D geometrical database for storing and retrieving information representative of 3-D models of the holographic scanning apparatus and processes under design; as well as a relational database for storing and retrieving information representative of geometrical and analytical models holographic laser scanning apparatus and processes under design. In addition, the CAD workstation includes a diverse array of computer programs which, when executed, provide a number of important design and analysis tools. Such design and analysis tools include, but are not limited to: 3-D geometrical modelling tools (e.g. AUTOCAD geometrical modelling software, by AutoDesk, Inc. for creating and modifying 3-D geometrical models of virtually every aspect of the holographic laser scanning apparatus and processes under design; robust mathematical modelling tools (e.g. MATHCAD 3.1 for Macintosh by MathSoft, Inc. of Cambridge, Mass.) for creating, modifying and analyzing mathematical models of the holographic scanning apparatus and processes under design; and spreadsheet modelling tools (e.g. EXCEL by Microsoft Corporation, or LOTUS by Lotus Development Corporation) for creating, modifying and analyzing spreadsheet-type analytical models of the holographic scanning apparatus and processes under design. For purposes of simplicity of expression, the above-described CAD workstation and all of its tools shall be collectively referred to as the “Holographic Scanner Design (HSD) workstation” of the present invention. Where necessary or otherwise appropriate, the functionalities and tools of the HSD workstation will be elaborated in greater detail hereinafter.

As indicated in Block A of FIG. 11A, the first step of the scanner design method involves the scanner designer creating within the geometrical database of the HSD workstation hereof, a geometrical model of the holographic laser scanner described above. Preferably, a 3-D geometrical model of the holographic laser scanner, including the scanning disc, is created, although a 2-D geometrical model will suffice in many applications where the symmetry of the scanning apparatus allows such simplification. A schematic diagram of the geometrical model of the holographic scanning disc under design is set forth in FIG. 9. Using this geometrical model of the scanning disc, the scanner designer then proceeds to index each i-th holographic facet on the scanning disc, as well as each j-th laser beam production module within the holographic scanning system. In the illustrative embodiment, this two-fold indexing step is carried out by assigning a unique number to each facet on the holographic scanning disc under design, and a unique number to each laser beam production module employed in the holographic laser scanning system of the present invention. The assigned facet and laser beam production module indices can then be used to identify which facets and laser beams are being referred to during the design and construction processes.

As indicated at Block B of FIG. 11A, the scanner designer then begins to create within the geometrical database of the HSD workstation, a geometrical model of the 3-D laser scanning pattern production process realized upon the multi-station laser scanning platform of the present invention. Owing to the symmetry of the laser scanning platform hereof, modelling of the complex laser scanning process of the present invention can be readily simplified by separately modelling the generation of each (i,j)th scanline within the 3-D laser scanning volume. Inasmuch as each (i,j)-th scanline is generated in substantially the same manner, except for the fact that a different (i-th) facet and a particular (j-th) laser beam are used to generate each scanline in the scanning volume, the substantially same geometrical optics model shown in FIG. 8A can be used to represent the production of each (i,j)th scanline.

In general, the geometrical optics model used to represent each (i,j)th scanline generation process employs a geometrical specification of the following structures: (1) the (i,j)-th scanline in physical relation to the stationary laser beam production module, the corresponding facet on the rotating holographic disc, the stationary beam folding mirror, and the base and scanning window of the scanner housing; and (2) the ray diagram tracing the path of the incident j-th laser beam from the laser beam production module, through the i-th facet, off the j-th beam folding mirror, and focusing onto the focal plane along which the (i,j)-th scanline extends. In order to eliminate the need for considering the reflection of the rays at the surface of the folding mirrors, and thus simplify the disk design process, a virtual holographic scanning disk 56 is defined relative to the real holographic scanning disk, as shown in FIGS. 8A and 8A1. This modelling technique allows the subsequent calculations to be made using the locations of the Beam Incident Point r₀ and the Inner Radii of the facets r_(i) in the virtual disk.

As part of the geometrical modelling process called for in Block B of FIG. 11A, numerous geometrical parameters and analytical equations defining relations therebetween need to be carefully defined by the scanner designer for use during the subsequent stages of the design process. In FIGS. 8B1 and 8B2, the parameters used to construct the geometrical model are defined. In FIGS. 8C1 and 8C2, the set of mathematical expressions used to establish important relations among certain of the parameters in the model are listed in a specified numerical order for future reference herein. The set of mathematical expressions set forth in FIGS. 8C1 and 8C2 provide an analytical model for the scanline production process of the present invention.

As indicated in FIGS. 8B1 and 8B2, the parameters used to construct the geometrical model of the (i,j)th scanline production process include:

(1) the radius to the Beam-Incident-Point on the holographic scanning disc, assigned the symbolic notated “r₀”;

(2) Scanline Separation between adjacent scanlines at the focal plane of the (i,j)-th scanline, assigned the symbolic notated “S_(SL)”;

(3) the Scanline Length (measured into the paper) for the (i,j)th scanline, assigned the symbolic notation “L_(SL)”;

(4) the Distance measured from the scanning disc to the focal plane of the (i,j)th scanline, assigned the symbolic notation “a_(i)”;

(5) the Distance from radius to the Beam-Incident Point r₀ to beam folding mirror, assigned the symbolic notated “L”;

(6) the Tilt Angle of the j-th beam folding mirror associated with the generation of the (i,j)-th scanline, assigned the symbolic notation “φ_(j)”;

(7) the Tilt Angle of the virtual scanning disc, assigned the symbolic notation “2φ”;

(8) the Lateral Shift of the Beam Incident Point on the virtual scanning disc, assigned the symbolic notation “Δx”;

(9) the Vertical Shift of the Beam Incident Point on the virtual scanning disc, assigned the symbolic notation “Δy”;

(10) the Distance from the rotation axis to the Beam Incident Point on the virtual scanning disc, assigned the symbolic notation r₀+Δx;

(11) the Distance from the Beam-Incident-Point on the virtual scanning disc to the focal plane within which the (i,j)th scanline resides, assigned the symbolic notation f_(i);

(12) the Diameter of the cross-section of the laser beam at the scanning disc, produced from the j-th laser beam scanning station, assigned the symbolic notation “d_(beam)”;

(13) the Angular Gap between adjacent holographic scanning facets, assigned the symbolic notation “d_(gap)”;

(14) the Outer Radius of the available light collection region on the holographic scanning disc, assigned the symbolic notation “r_(outer)”;

(15) the Inner Radius of the available light collection region on the holographic scanning facet, assigned the symbolic notation “r_(inner)”;

(16) one-half of the Depth of Field of the (i,j)th scanline, assigned the symbolic notation “δ”;

(17) the Distance from the maximum read distance (f_(i)+δ=5”) to the Inner Radius r_(i) of the scanning facet, assigned the symbolic notation“C”;

(18) the Outer Ray Angle measured relative to the normal to the i-th holographic facet, assigned the symbolic notation “α”;

(19) the Inner Ray Angle measured relative to the normal to the i-th holographic scanning facet, assigned the symbolic notation “γ”;

(20) the Light Collection Angle, measured from the focal point +δ of the i-th facet to the light collection area of the scanning facet, assigned the symbolic notation “β”;

(21) the intersection of the beam folding mirror and line C, assigned the symbolic notation “x” (x measured from rotational axis of disk);

(21) the intersection of the beam folding mirror and line C, assigned the symbolic notation “y” (y measured from plane of disk);

(22) the Distance measured from the Inner Radius to the point of mirror intersection, assigned the symbolic notation “D”;

(23) the Distance measured from the base of the scanner housing to the top of the j-th beam folding mirror, assigned the symbolic notation “h”;

(24) the Distance measured from the scanning disk to the base of the holographic scanner, assigned the symbolic notation “d”;

(25) the Focal Length of the i-th holographic scanning facet from the scanning facet to the corresponding focal plane within the scanning volume, assigned the symbolic notation “f_(i)”;

(26) Incident Beam Angle measured with respect to the i-th holographic facet surface, assigned the symbolic notation “A_(i)”;

(27) Diffracted Beam Angle measured with respect to the i-th holographic facet surface, assigned the symbolic notation “B_(i)”;

(28) the Angle of the j-th laser beam measured from the vertical, assigned the symbolic notation “−α”;

(29) the Scan Angle of the diffracted laser beam produced by i-th facet, assigned the symbolic notation “θ_(si)”;

(30) the Scan Multiplication Factor for the i-th holographic facet, assigned the symbolic notation “M_(i)”;

(31) the Facet Rotation Angle for the i-th holographic facet, assigned the symbolic notation “θ_(roti)”;

(32) Adjusted Facet Rotation Angle accounting for deadtime, assigned the symbolic notation “θ_(roti)”;

(33) the Light Collection Efficiency factor for the i-th holographic facet, normalized relative to the 16th facet, assigned the symbolic notation “ξ_(i)”;

(34) the Total Light Collection Area for the i-th holographic facet, assigned the symbolic notation “Area Total_(i)”;

(35) the Beam Speed at the Center of the (i,j)th Scanline, assigned the symbolic notation “V_(center)”;

(36) the Angle of Skew of the diffracted laser beam at the center of the i-th holographic facet, assigned the symbolic notation “θ_(skew)”;

the Maximum Beam Speed of all laser beams produced by the holographic scanning disc, assigned the symbolic notation “V_(max)”;

(38) the Maximum Beam Speed of all laser beams produced by the holographic scanning disc, assigned the symbolic notation “V_(min)”;

(39) the ratio of the Maximum Beam Speed to the Minimum beam speed, assigned the symbolic notation “V_(max)/V_(min)”; and

(40) the deviation of the light rays reflected off the parabolic light reflecting mirror beneath the scanning disc, from the Bragg angle for the facet assigned the symbolic notation “δ_(e)”.

Notably, certain of the above-defined parameters are assigned initialized (i.e. assumed) values, whereas other parameters are computed using the mathematical expressions set forth in FIGS. 8C1 and C2. Exactly which parameters are initialized, and which are computed, and in what order, will be explained hereinafter.

As indicated as Block C in FIG. 11A, the next step of the scanner design process involves using the geometrical parameters and mathematical expressions of FIGS. 8B1 through 8C2, and the “spreadsheet” modelling tool of the HSD workstation in order to create an analytically-based Scanline Production Model which describes the physical production of each (i,j)th scanline within the 3-D scanning volume of the present invention. As mentioned above, suitable spreadsheet-computer programs for carrying out this stage of the disc design process include, for example, EXCEL® from Microsoft, Inc., and LOTUS® from the Lotus Development Corporation. The function of the spreadsheet modelling/analysis tool is to provide a network-type information storage structure, within which the mathematical expressions of the spreadsheet-based Scanline Production Model can be embodiment in a manner well known in the spreadsheet computing art. With functional links established among the information storage nodes within the underlying information storage network of the spreadsheet computer program, the scanner designer is thereby permitted to modify one or more parameters of the analytical model and analyze how other parameters within the model change, permitting “what if ” analysis with respect to the various parameters comprising the analytical Scanline Production Model. Notably, the display format for the spreadsheet tool will vary from embodiment to embodiment, and in itself, is not an important aspect of the present invention.

As indicated at Block D of FIG. 11A, the next step of the disc design process involves the scanner designer specifying assumed (i.e. initial) values for a number of parameters in the spreadsheet-type analytical model of each (i,j)th scan line production process. In the illustrative embodiment, these assumed parameters include: the radius to Beam-Incident-Point on the holographic scanning disc r₀, which by design is the same for each (i,j)-th scanline (mainly determined by the size of the disk); Scanline Separation S_(SL) of adjacent scanlines at the focal plane of the (i,j)-th scanline, and “ScanLine Length” for the (i,j)-th scanline L_(SL) (both established by the user application requirements); Distance from the Beam-Incident-Point to the Beam Folding Mirror, L (usually chosen to be as small as possible to minimize scanner volume); Tilt Angle of Beam Folding Mirror associated with the generation of the (i,j)-th scanline, φ; the distance from the scanning disc to the focal plane of the (i,j)-th scanline, f_(i); the cross-sectional diameter of the laser beam d_(beam) produced from the j-th laser beam scanning station (established by spot size requirements at the focal planes); the Angular Gap between adjacent holographic scanning facets, d_(gap), and the width of the Home-Pulse Gap d_(gap)max; the Outer Radius of the light collection region on the holographic scanning disc, r_(outer); one-half (½) of the Depth of Field of the (i,j)th scanline, δ; the Distance from the holographic scanning disc to the Base of the holographic laser scanner, d; and the Deviation Angle δ_(e), from the Bragg angle. Notably, the assumed values for these parameters are selected using both heuristics and experience associated with each particular parameter. Typically, such heuristics are obtained from design criteria and scanner application requirements of the end user. Such heuristics will be briefly discussed below.

In general, the diameter of the holographic scanning disk can be initially selected on the basis of estimates of the required Lambertian light collection efficiency of the holographic scanning facets, and the useable optical power producible from commercially available VLDS. In the illustrative embodiment, a 220 mm diameter was selected for the holographic scanning disk. This assumed figure was a compromise between maximizing the diameter of the scanning disk in order to maximize the Lambertian light collection efficiency, and minimizing the diameter of the scanning disk to provide a more compact scanner housing design while minimizing mechanical problems. Then initial values were selected for the Angular Gap d_(gap) between adjacent holographic facets, and the width of the Home-Pulse Gap d_(gap)max.

Once assumed values have been established for the above-described parameters, the balance of the “initializable” parameters in the spreadsheet-based Scanline Production Model can be determined using fundamental geometric and/or trigonometric equations. For example, the geometerical parameters Δx, Δy, indirectly specifying the location of the virtual image of the scanning disk created by the folding mirror, can be established (i.e. initialized) by applying the Laws of Reflection. The location of the Scanline Center Points (x,y,z) can be determined from the initialized Scanline Spacing S_(SL), the assumed Focal Distances for the scanning facets f_(i), and the symmetry of the axially centered scan pattern of the illustrative embodiment. In order to allow symbol reading at the limit of the depth of field for each scanning plane, each focal distance f_(i) to the (i,j)th specified scanline should be slightly extended (e.g. by 5 inches).

Having created at Block D of FIG. 11D, a spreadsheet model for the (i,j)th scanline production process, the scanner designer then uses the spreadsheet tool of the HSD workstation to automatically compute the value of parameters in the Scanline Production Model using dependent parameters which are known by either assumption (i.e. initialization) or numerical evaluation. While the order in which particular parameters of the analytical model are numerically evaluated (due to parametric dependency) is generally transparent to the operator of the spreadsheet tool, the scanner designer of the spreadsheet-based Scanline Production Model must know the relational dependency among the various parameters in the analytical structures thereof so that the information nodes and fields underlying the spreadsheet model can be properly structured. Thus, for purposes of clarity and completeness, the computational steps carried out within the spreadsheet-based Scanline Production Model of the present invention during the scanner design process will be described in detail below. It is understood, however, that in practice, many of these steps will be transparent to the scanner designer inasmuch as he or she will need to provide particular inputs into the spreadsheet-based Scanline Production Model, and the Model will automatically produce for display, parameters of relevance to the scanner design process.

Having assumed initial values for the above-described parameters at Block D in FIG. 11A, the next step of the design process hereof, indicated at Block E thereof, is to use Expression No. 17 in FIG. 8C2, the mathematical expressions dependent therefrom (Nos. 16,15,14,13,12, and 1) and the assumed dependent parameters within the Scanline Production Model to numerically evaluate the Scan Angle θ required to produce the specified ScanLineLength L_(SL) associated with each i-th holographic facet. As reflected by this set of functionally dependent expressions, the Scan Angle θ_(si) required to produce the specified ScanLine Length L_(SL) is determined solely by the selection of assumed values for the parameters indicated in Expression Nos. 17,16,15,14,13,12, and 1.

A few observations at this point will be helpful. First, for a given Scan Angle θ_(si), it is possible to adjust the Scanline Length L_(LS) at the focal plane specified by focal length f_(i) by simply increasing or decreasing the Scanline Multiplication factor M_(i), which is dependent upon the Angle of Incidence A_(i) and the Angle of Diffraction B_(i). Secondly, the sum of the Adjusted Facet Rotation Angles, θ′_(rot), for all of the facets (including the sweep angle associated with dead time, θ_(dead)=d_(beam)/r₀+d_(gap)/r₀) should equal approximately 358.5 degrees in an optimum design. This allows for 1.5 degrees extra for the large interfaced gap used for the home pulse. If this total is more than 358.5 degrees, the proposed design will be inadequate. If the total is less than 358.5 degrees, the beam speeds will be unnecessarily high.

As indicated at Block F in FIG. 11A, the next step of the scanner design step is to numerically evaluate, for each i-th scanning facet, the Diffraction (Outgoing) Beam Angle B_(i) associated with the i-th scanning facet. This computation is carried out using Expression No. 13 in FIG. 8C2 and previously assumed and evaluated parameters specified by this mathematical expression. Completion of this step produces a Diffracted (Outgoing Beam) Angle B_(i) for each of the 16 facets for the scanning disk under design. Notably, both Angles of Incidence and Diffraction A_(i) and B_(i) must provide the required ScanLine Length L_(SL), with no excess. These is a subtle relationship between these angles and the speed of the laser beam being moved along the scanline during scanner operation. In particular, if the angle of incidence A_(i) is increased below a particular value, then the scan pattern may not be adequate for the application at hand. On the other hand, if the angle of incidence A_(i) were decreased, the scan pattern may be longer than necessary, resulting in higher than necessary scan beam velocities. The correct value of A_(i) will minimize the beam velocity at the focal planes of each of the scan patterns, which in turn minimizes the required electronic-bandwidth for the signal circuitry connected to the photodetectors.

After completing this computational step, the scanner designer uses a MATHCAD-based program running on the HSD workstation to numerically evaluate at Block G, for each i-th holographic facet, the relative Light Diffraction Efficiency Factor thereof H_(i) to light of a particular polarization state. In order to compute these parameters {H_(i)}, the spreadsheet-based Scanline Production Model employs a computer sub-program to perform a light diffraction efficiency analysis upon each of the scanning facets under design, and computes therefrom, the total out-and-back light diffraction efficiency of the i-th scanning facet relative to the total out-and-back light diffraction efficiency of the 16th scanning facet, to provide a normalized light diffraction efficiency measure for the i-th facet. This computational process involves theroetically deriving mathematical expressions representative of the light diffraction efficiency of each scanning facet, that is, given the polarization state and light detection scheme employed in the particular scanner embodiment at hand. The details of this analysis will be explained below.

In FIG. 10A1, a geometrical optics model is provided for relative light diffraction efficiency (H_(i)) calculations in the case where the incident laser beam is produced from VLD generating an S polarized light beam, and no polarizing filter is provided in front of the photodetector of each scanning station. This figure drawing shows the optical paths along which the laser beam is diffracted, reflected, diffracted, focused and transmitted without substantial diffraction during the laser beam scanning and light collection process of the present invention. The transformation of polarization states during this process is described in FIG. 10A. The mathematical expression used to compute the light diffraction efficiency of each i-th scanning facet to S and P polarized light is derived from the geometrical optics model shown in FIGS. 10A2 and 10A3 and the analytical model (i.e. tool) is described in FIGS. 10B through 10E2.

In the preferred embodiment, the analytical model of FIGS. 10B through 10E2 is realized using MATHCAD 3.1 mathematical modelling program available from MathSoft, Inc, of Cambridge, Mass. The mathematical expression derived for the total out-and-back diffraction efficiency for an S-polarized outgoing beam incident on the scanning disk (including Fresnel reflection losses and other internal losses of 10%) is notated at T_(s)[Δn_(i)] and is set forth in Expression No. 13 in FIG. 10C2. Notably, in the geometrical optics model used to support the diffraction efficiency analysis, angle of incidence θ_(i) and angles of diffraction θ_(i) are defined differently from angle of incidence A_(i) and angle of diffraction B_(i) used in the Scanline Production Model described above. This fact is based solely on historical reasons, and is of little significance. However, such angles are mathematically related angles. Angles A_(i) and B_(i) are complements of angles θ_(i) and θ_(d), respectively, and thus A_(i)=90°−θ_(i), and B_(i)=90°−θ_(d). As shown, this mathematical expression depends on the S polarization and P polarization diffraction efficiencies of the i-th holographic facets on the disk which, in general, are functions of various parameters, including the incidence angle θ_(i) and the modulation index (i.e. modulation depth or fringe contrast) Δn_(i) of the holographic facet, assuming the thickness of the emulsion T is maintained constant across the facet. However, by fixing (assuming a value for) each of the variables in the expressions for these diffraction efficiencies, except Δn_(i), the expressions for these diffraction efficiencies can be made simply a function of Δn_(i). In such circumstances, the light diffraction efficiency can be set by simply controlling the modulation index Δn_(i) during facet construction in a holographic laboratory. In a manner well known in the art, the modulation index Δn_(i) can be controlled by properly exposing and processing the dichromated gelatin (DCG) used to record the fringe structure of the scanning facet. The necessary exposure control can be achieved by controlling the power of the construction laser beam and/or time duration that the laser beam is incident on the gelatin during the holographic recording operation.

Expression No. 14 in FIG. 10C2 sets forth how to compute the relative light diffraction efficiency factor H_(i) for each facet as a function of the total out-and-back diffraction efficiencies T_(s)[Δn_(i)] for each -th and 16-th scanning facets. However, it will be appropriate to first describe techniques that can be used to derive mathematical expressions No. 11 and 12 in FIG. 10C2 for S and P polarization diffraction efficiencies in the holographic laser scanner system under design.

Foremost, it is important to be clear as to the referencing of the S and P polarization directions when deriving mathematical expressions for the S and P light diffraction efficiencies of holographic scanning facets. In accordance with convention, these polarization directions are defined with respect to the plane of incidence, namely: the “S polarization direction” is defined to reside in the direction perpendicular to the “plane of incidence”; whereas the “P polarization direction” is defined to reside in the directional parallel to the plane of incidence. The “plane of incidence” is defined as that plane containing both the normal to the facet surface, at the point of incidence of the incident ray, and the incident ray. Also, it is important to keep clear in mind that such polarization directions refer to the direction in which the Electric Field (or E-Field) vector associated with the spherical wavefront of the incident laser beam acts on static electric charges during electromagnetic wave propagation.

To avoid confusion with the S&P terms introduced in a later section concerning the astigmatic sources in a VLD, the terms “S wave-Component” and “P wave-component” will be introduced to define the above polarization directions of the incident laser beam. The term “S wave-component” is used to specify the component of the resultant spherical wavefront emanating from the laser beam production module and falling incident upon the scanning disc, and having an E-field vector oriented in the S polarization direction. Similarly, the term “S polarized wave-component” is used to specify the component of the resultant spherical wavefront emanating from the laser beam production module and falling incident upon the scanning disc, and having an E-field vector oriented in the P-polarization direction. According to such definitions, both the S and P cylindrical wavefronts comprising the resulting spherical wavefront of the incident laser beam will contribute to the S wave-component, whereas both the S and P cylindrical waveforms comprising the resulting spherical wavefront of the incident laser beam will contribute to the P wave-component.

The model used herein to describe the total out-and back diffraction efficiency of S and P wave-components of the incident laser beam during scanning operations is based upon the theory of electromagnetic-wave coupling within thick holographic structures, which was originally described in the celebrated paper entitled “Coupled Wave Therory for Thick Hologram Grating” by Herwig Kogelnik, supra. The two basic assumptions upon which this theory requires for application are: (1) that the thickness T of the emulsion in which the holographic fringe structures are formed is substantially greater than the wavelength of the incident wavefront; and (2) that the incident wavefront can be approximated by a parallel wavefront. The first assumption holds true for out volume-transmission type holograms, from which each holographic facet on the scanning disc hereof is made. The second assumption also holds true for the case where the spherical wavefront incident the input surface of the hologram has a very large radius of curvature over the incident surface, which is true in the present invention.

In FIG. 10C1, a set of mathematical expressions are provided. These mathematical expressions are used to derive light diffraction efficiency expressions identified by Expressions 11, 12 and 13 in FIG. 10C2. Expression No. 1 through 3 in FIG. 10C1 relate internal angles to external angles through Snell's Law. Expressions 4 and 5 describe attributes of the slanted fringe structure of the holographic light diffraction facet sandwiched between the glass support plates of the scanning disc. These expressions have been derived by applying Snell's Law at the interfacial surfaces of the scanning disc, and using the well known Grating Equation to derive the variable spatial frequency fringe structure of the scanning facet. Expressions No. 6 through 10 in FIG. 10C1 relate the coupling of incident and diffracted wave to the internal angle α and fringe slant angle θ associated with the scanning facet, and are derived from the fundamental work of Kogelnik, supra. Notably, the obliquity factors set forth in Expressions No. 6 and 7 are expressed as a function of the internal angle α and fringe slant angle θ for a particular scanning facet, and determine how well optical input power is diffracted in the various diffraction orders. While the total out and back light diffraction efficiencies defined by Expressions No. 11 and 12 are functions of modulation depth, it is understood that such light diffraction efficiency expressions can be derived as a function of angle of incidence, as required in Bragg Sensitivity Analysis, by fixing the modulation index, Δn (i.e. Δn=n, in graphical plots), and allowing δ, in Expression No. 9 to vary.

Notably, Expressions 11 and 12 in FIG. 10C2 include three terms. The first term in both of these mathematical expressions is a function of factors N(Δn) and S(Δn) defined by Expression Nos. 8 and 10 in FIG. 10C1, and relates to the transmission of light by way of the process of light diffraction, as explained in terms of the Coupled Wave Theory described by Kogelnik, supra. The second term in both of Expressions No. 11 and 12 is a Fresnel transmission term t_(s), and relates to the transmission of S or P polarized light through the scanning facet by way of the phenomenon of Fresnel transmission. The third term in both Expressions No. 11 and 12 is an estimated internal loss term (1-0.1), and relates to an estimate of 8% loss due to scattering and absorption in the gelatin and 2% Fresnel reflection loss at the gelatin/glass interfaces. Collectively, these three terms specify the light diffraction efficiency of the i-th scanning facet to S or P polarized light incident thereto.

Thus, by embracing the terms of Expressions 11 and 12, mathematical Expression No. 13 in FIG. 10C2 is used to calculate the total out-and-back diffraction efficiency for an S-polarized outgoing beam. In practicing the scanner design method of the present invention, this light diffraction efficiency expression (Expression No. 14) is inserted in the proper cells of the spreadsheet-based Scanline Production Model running on the HLD Workstation. While the S and P polarization diffraction efficiencies E_(s)[Δn_(i)]and E_(P)[Δn_(i)], and the total out-and-back diffraction efficiency for an S-polarized outgoing beam T_(s)[Δn_(i)], are plotted for facet Nos. 1 and 16 in FIGS. 10E1 and 10E2, respectively, for different values of modulation index Δn_(i), the spreadsheet Model in practice uses the value of modulation index Δn_(i) which maximizes T_(s)[Δn_(i)]. Once this value of Δn_(i) is found and the maximum T_(s)[n₁] computed for each scanning facet, then the out-and-back diffraction efficiency of each i-th facet relative to facet No. 16 (i.e. the relative light diffraction efficiency, H_(i)) is computed for each i-th scanning facet and stored along with the value of Δn_(i) used to compute this parameter value. H is the relevant parameter used in the spreadsheet based Scanline Production Model of the design process.

Having described the case where no cross-polarizer is used before the photodetector, it is appropriate to now consider the case when using a cross-polarizer before the photodector. This technique is used to combat glare from glossy substrates and/or overcoats. In such a case, the light diffraction efficiencies of the scanning facets on the scanning disc will be modified to accommodate the fact that light of one polarization is diffracted by the facets during scanning, but only the return light of the orthogonal polarization state diffracted by the facet will pass through the crossed polarizer to the detector. In this case, the light diffraction efficiency analysis to be used for computing H_(i) is described in FIGS. 10F through 10I2. In all but a few respects, the light diffraction efficiency analysis for the cross-polarizer case is quite similar to the case without cross-polarizer. The major difference in the analysis is that the mathematical expression for total out and back light diffraction efficiency for the i-th facet does not peak at the same value of modulation index Δn as Ts(Δn) in the previous case. Thus, as shown in Expression No. 13 in FIG. 10H2, the mathematical expression for total out and back light diffraction efficiency for either S or P polarized outgoing light E_(t)[Δn] is defined as the product of the S and P light diffraction efficiencies, rather than the product of the S diffraction efficiency and the average of the S and P diffraction efficiencies, as shown in Expression 13 in FIG. 10C2. In practicing the scanner design method of the present invention, this light diffraction efficiency expression (No. 14) is inserted in the proper cells of the spreadsheet-based Scanline Production Model running on the HLD Workstation. While the S and P polarization diffraction efficiencies E_(s)[Δn_(i)]E_(p[Δn) _(i)], and the total out-and-back diffraction efficiency for an S-polarized outgoing beam E_(t)[Δn_(i)] are plotted for facet Nos. 1 and 16 in FIGS. 10I1 and 10I2, respectively, for different values of modulation index Δn, the spreadsheet Model in practice uses the value of modulation index Δn_(i) which maximizes E_(t)[Δn_(i)]. Once this value of Δn_(i) is found and the maximum E_(t)[Δn₁] computed for each i-th scanning facet, then the out-and-back diffraction efficiency of each i-th facet relative to facet No. 16 (i.e. The relative light diffraction efficiency, H_(i)) is computed for each i-th scanning facet and stored along with the value of Δn_(i) used to compute this parameter value. H_(i) is the relevant parameter used in the spreadsheet based Scanline Production Model.

At Block H in 11B, the spreadsheet-type Scanline Production Model proceeds to compute for each i-th scanning facet, the Relative Light Collection Efficiency Factor ζ_(i). Notably, this parameter is computed using Expression No. 18 in FIG. 8C2 and the various parameter values specified therein which have been previously assumed and evaluated. In the present invention, the Total Light Collection Efficiency of each holographic facet is substantially the same (equal) when measured from its focal point f_(i). As indicated in Expression No. 18, the “relative” Light Collection Efficiency factor ζ_(i) for each i-th facet comprises three terms: the first term is a Lambertian geometrical term; the second term is a projected area term; and the third term is a relative light diffraction efficiency term (H_(i)). The Lambertian geometry term is formulated in terms of the focal length of the facet, f_(i), and the focal length of facet No. 16, f₁₆. The projected area term is formulated in terms of the diffracted beam angle of the i-th scanning facet, B_(i), and the diffracted beam angle of facet No. 16, B₁₆. The relative light diffraction efficiency for the i-th scanning facet, H_(i), is formulated in terms of the total out-and-back light diffraction efficienies for the i-th facet and the 16th facet, as described in great detail above. Notably, inasmuch as the relative light diffraction efficiency for each i-th facet H_(i) is a function of the facet's modulation index, Δn_(i), which maximizes H_(i), the relative Light Collection Efficiency Factor for each i-th scanning facet, ζ_(i), is also a function of the modulation index Δn, a parameter which can be controllably realized during facet construction in the laboratory as well as on the production line. These three terms in Expression No. 18 of FIG. 8C2 represent three critically important design considerations necessary to construct a scanning disc, wherein each facet has substantially the same Lambertian light collection efficiency. In the next step of the design process, it remains to be taught how this objective can be carried out while using substantially all of the available surface area on the scanning disc.

Having calculated the Light Collection Efficiency Factor ζ_(i) for each scanning facet on the disc under design, the spreadsheet-based Scanline Production Model proceeds to Block I of FIG. 11B where it uses Expression No. 19 in FIG. 8C2 to calculate the Total Light Collection Area of each i-th scanning facet, Area_(i), on the scanning disk under design. Notably, the first term in Expression No. 19 reflects the fact that all of the available light collecting area between the outer radius and inner radius (i.e. adjacent the disk support hub) is used in apportioning light collecting surface area to each scanning facet on the disk. The second term in Expression No. 19 of FIG. 8C2 reflects the fact that the total light collecting surface area of each facet Area_(i) is computed by weighing the total light collecting surface area available on the scanning disk by an “equalized” light collecting efficiency factor. As indicated by Expression No. 19 of FIG. 8C2, this “equalized” light collecting efficiency factor is computed by dividing the i-th light collecting efficiency factor by the sum of all light collecting efficiency factors for all of the sixteen facets. Thus, each holographic facet on the scanning disc is capable of collecting substanially the same amount of reflected laser light and directing it onto the parabolic light focusing mirror beneath the disk, independent of the location of the scanned code symbol within the scanning volume of the system. In practical terms, this means that each facet will focus substantially the same amount of light onto a photodetector, independent of whether the scanned code symbol resided at the farthest focal plane or the closest focal plane in the scanning volume.

At Block J in FIG. 11B, the scanner design uses the spread-sheet based Scanline Production Model to determine, for each facet, the minimal value for the facet inner radius r_(i) that allows the scanner housing height h to be equal to the desired scanner housing height h_(desired), specified by customer requirements. This step of the design process involves using the optimized parameters determined above to determine the set of inner radius parameter values, {r_(i)}, for all facets on the scanning disk which provides the desired scanner housing height h_(desired), required by the system specifications, below which the beam folding mirrors must be contained while ensuring the production of the prespecified scanning pattern. Before describing the reiterative evaluation procedure used to find the set of minimum inner radius parameter values {r_(i)} which satisfy the necessary conditions to ensure that h=h_(desired), will be helpful to first describe how the inner radius r_(i) for each facet can be found in terms of other geometrically related parameters in the system.

As illustrated in FIG. 8A, the angle (i.e. B−β) in FIG. 8A1 of the ray going to the innermost part of the light collection portion of each i-th facet is calculated using the ray projected from the maximum reading distance point at the center of each scanline to the inner radius of the i-th facet on the virtual scanning disk. The intersection of this ray and the beam folding mirror is used to establish the height of the folding mirror, y_(j). Notably, only the ray giving the maximum mirror height is used to set the final mirror height. As described in Expression No. 11 in FIG. 8C1, this dimension y_(j), plus the dimension d beneath the disk for the light collection optics, establishes the overall height of the scanner housing, h.

The tilt angle of the beam folding mirror θ_(j) is one of the parameters that can be varied (i.e. assumed) to arrive at a “best” scanner design. It has been found that a large tilt angle (away from the scan beams) results in a shorter housing size, but requires very shallow exit angles for the beams leaving the holographic scanning disk. This makes the scanning disk difficult to fabricate and lowers the overall light diffraction efficiency and thus total light collection efficiency thereof. It also results in unnecessarily high beam speeds. A small tilt angle will result in better exit angles for the beam leaving the holographic disk, but results in a taller scanner housing size and a reduction in the scan lenghts of the scan lines for the 16 facet scanning disk of the illustrative embodiment. After several reiterations, an optimum tilt angle θ_(j) for the beam folding mirror was established at 16 degrees from the vertical.

In the reiterative evaluation procedure used to find the minimum r_(i), the goal is essentially to minimize r_(i) for all facets as this will ensure that the maximum amount of available light collecting space on the scanning disc is utilized for light collection. If the inner radius parameter r for each facet minimized while all other conditions are being satisfied, then the amount of laser light reflected off the scanned symbol and collected by the facets on the rotating scanning disc will be maximized, thereby producing strong scan data signals at the photodetectors of the system. Also, as shown by Expressions No. 11 and 10 in FIG. 8C1, minimizing r_(i) for each scanning facet causes the height of the beam folding mirrors to be greater, necessitating a scanner housing with an increased height dimension. Thus, adjustment of the inner radius of the facets has significant effects on other important geometerical parameters in the holographic scanning system.

In general, the reiterative evaluation procedure supported by the spreadsheet-based Scanline Production Model typically comprises a number of design cycles, each of which can be identified by an assigned cycle index k=1,2,3,4,5, . . . , 6,7,8, etc. During the (k=1) cycle, the disc designer uses Equations No. 4 through 11 in FIG. 8C1 to compute the beam folding mirror height, h. In order to compute an initial value for h (i.e h_(i)) using an initial value for each r_(i), an initial value for each r_(i) (e.g. 1.0 inch)is selected for the first run of calculations (e.g. r_(i) =1.0 r₂ =1.0, . . . , r₁₆=1.0 ). The result of this cycle of computations is a set of scanner housing height values, (e.g. h_(i)=12.0 inches, h₂=12.5 inches, . . . , h₁₅=15.0 inches, h₁₆=12.3 inches ) where h₁₅=15.0 inches in the illustrative example is the maximum height computed for the initial value for each r_(i).

If none of the computed height values are equal to or below h_(desired), then during the (k+1) cycle each inner radius parameter r_(i) is incremented by a very small amount (e.g. +0.2 inch) and the scanner height parameter h_(i) is recalculated for each value of facet inner radius r_(i). The set of scanner height values are then analyzed by the scanner designer to determine which values of r_(i) yielded scanner housing height (h_(i)) values less than or equal to h_(desired). Each value of r_(i) that yielded a scanner housing height h_(i) value less than or equal to h_(desired), is stored in memory of the HSD workstation and fixed in subsequent computational cycles of the reiterative process. Each value of r_(i) that did not yield a scanner housing height h_(i) value less than or equal to h_(desired), is changed in subsequent computational cycles of the reiterative process.

If all of the computed height values are equal to or above h_(desired), then during the (k+1) cycle, then each inner radius parameter r_(i) is incremented by a very small amount (e.g. +0.2 inch) and the scanner height parameter h_(i) is recalculated for each value of facet inner radius r_(i). The set of scanner height values are then analyzed by the scanner designer to determine which values of r_(i) yielded scanner housing height (h_(i)) values less than or equal to h_(desired). Each value of r_(i) that yielded a scanner housing height h_(i) value less than or equal to h_(desired), is stored in memory of the HSD workstation and fixed in subsequent computational cycles of the reiterative process. Each value of r_(i) that did not yield a scanner housing height h_(i) value less than or equal to h_(desired), is changed in subsequent computational cycles of the reiterative process.

If all of the computed height values are equal to or above h_(desired), then during the (k+1) cycle, then each inner radius parameter r_(i) is incremented by a very small amount (e.g.+0.2 inch) and the scanner height parameter h_(i) is recalculated for each value of facet inner radius r_(i). The set of scanner height values are then analyzed by the disc designer to determine which values of r_(i) yielded scanner housing height (h_(i)) values less than or equal to h_(desired). Each value of r_(i) that yielded a scanner housing height h_(i) value less than or equal to h_(desired), is stored in memory and fixed in subsequent computational cycles of the reiterative process. Each value of r_(i) that did not yield a scanner housing height h_(i) value less than or equal to h_(desired), is changed in subsequent computational cycles of the reiterative process.

The reiterative evaluation process progresses as described above until a value for each inner radius r is found which yields a scanner housing height h which is less than or equal to the desired scanner housing height h_(desired). When this point in the process is reached, then the spreadsheet-based Scanline Production Model will have determined a set of inner radius parameter values {r_(i)} for the facets on the scanning disk under design.

At Block K in FIG. 11B, the spreadsheet-based Scanline Production Model uses the assumed value for r_(outer), the optimized set of parameter values {r_(i)}, and the previously computed set of light collection efficiency value {ζ_(i)}, to compute the net light collecting surface area for each i-th scanning facet, Area_(i), such that each and every facet collects at its photodetector substantially the same amount of light from its corresponding scanline, while substantially all of the surface area available on the scanning disc is utilized for light collection purposes. In order to ensure that such conditions are satisfied during this set of parameter computations, Expression No. 19 in FIG. 8C1 includes mathematical structure which defines a term for surface area computation which in conjunction with the proportioned hologram efficiency factor (i.e.ζ_(i)/Σζ_(i))), will provide light collection efficiency equalization (i.e. normalization). Upon completion of this step, a set of facet surface areas {Area_(i)} is produced.

At this stage of the process, the spreadsheet-based Scanline Production Model holds for each facet a set of geometrical parameters which, in theory, would be sufficient to construct a scanning disc capable of producing the prespecified scanning pattern during the initial stage of the design process. Specifically, this proposed set of geometrical parameters comprises: a set of facet Rotation Angle values {θ′_(roti)} for the holographic facets; a set of inner radius values {r_(i)} for the holographic facets; a set of Total Light Collection Surface Areas {Area_(i)} for the holographic facets; a set of Focal Length values {f_(i)} for the holographic facets; and a set of modulation index values {Δn_(i)} for the holographic facets. Collectively, these parameters shall be referred to as “construction parameters” as they are used to construct the facets on the holographic scanning disk. Notably, the subset of construction parameters {θ′_(roti), r_(i), Area_(i)} provides a geometrical specification for the i-th scanning facet which, in general, has irregularly shaped boundary characteristics constrained by these construction parameters and the condition that all of the available surface area on the disk be utilized for light collection.

Having found a set of facet parameters which will produce the prespecified laser scanning pattern, while satisfying scanner housing design constraints, it nevertheless is essential to determine whether the set of facet construction parameters, derived from the scanner design process, can be physically laid out on the available surface area of the scanning disk whose geometry has been previously bounded by outer radius r_(outer).

During the facet lay out verification stage of the design process indicated at Block L of FIG. 11B, the scanner designer tries to physically layout on the surface of the scanning disc, each of the geometrically-specified holographic facets in a facet order which allows maximum use of the disk surface area. Inasmuch as each facet has been “loosely” constrained by its construction parameters {θ′_(roti), r_(i), Area_(i)}, the disk layout designer is accorded a degree of freedom in which to specify the perimetrical boundaries of each facet so that substantially all of the available surface area on the disk is occupied by the facets, while the construction parameters {θ′_(roti), r_(i), Area_(i) } for each i-th facet are satisfied. When the disk layout designer has achieved this objective, then the complete set of construction parameters {θ′_(roti),r_(i), Area_(i)f_(i),Δn_(i),A_(i), B_(i)} for i=1,2, . . . ,16 can be used to make the designed scanning disk.

In the preferred embodiment, a geometrical modeling tool, such as AUTOCAD, supported by the HSD workstation is used to geometrically model each scanning facet and layout the same on the scanning disk while satisfying several global constraints, namely: (1) that substantially all of the light collecting surface area available on the scanning disk is utilized; (2) that at the end of each scanline sweep, all or almost all of the light collection surface area associated with the corresponding facet is disposed immediately above the parabolic collection mirror (i.e. light collection element) to maximize light detection at the photodetector; and (3) that all incoming light rays reflected from a scanline produced by the j-th scanning station, strike its associated beam folding mirror and are collected by the same scanning facet which produced the scanline, to avoid signal clipping and thus ensuring maximal SNR at the photodetector. Notably, during this stage of the scanner design process, a set of construction parameters {θ′_(roti), r_(i)Area_(i)} for all values of i cannot be changed or altered for any of the holographic facets, but rather must be maintained as constants throughout the procedure. Specifically, the facet layout procedure is carried out by adjusting the boundary lines for each facet, while satisfying the above described constraints and facet parameters {θ′_(roti), r_(i), Area_(i)}.

If the scanner designer can successfully layout the facets on the disc using the tools available within the HSD workstation, then the disc designer proceeds to the final stage of the design process indicated at Block M where designed scanner is analyzed against its design performance criteria (e.g. equalized light collection efficiency among the facets, etc.). This stage of the process is carried out using various analytical tools available in the HSD workstation. For example, the HSD workstation provides the scanner designer with a tool for computing the Lambertian light collection efficiency, E_(L), of each facet on a designed scanning disc. The purpose of this tool is to allow the scanner designer to quickly compute the Lambertian light collection efficiency of each i-th facet on a designed scanning disc, and determine whether such light collection efficiency measures are substantially equal for each facet on the designed scanning disc. If not, then the scanner designer can return to the spreadsheet-based Scanline Production Model and modify the disc and/or scanner design until acceptable performance parameters are obtained for the application at hand. Below, the structure and function of the Lambertian light collection efficiency measuring tool will be described in greater detail.

In FIGS. 10J through 10L1, a geometrical optics model (I.e. Lambertian Radiator Model) is presented for calculating the Lambertian ligh collection efficiency, E_(L), of each i-th facet on a scanning disc produced using the disc design procedures of the present invention. The parameters associated with the Lambertian Radiator Model are geometrically defined in FIG. 10K. The set of equations listed in FIG. 10L1 define relationships among certain of the parameters in the model. Notably, the E_(L) calculation procedure described herein does not include factors related to diffraction efficiencies, holographic disk transmission characteristics for off-Bragg angles, mirror reflectances, window transmission characteristics and bar code label reflectances. It is understood that all of such parameters must be taken into account to determine the total light collection efficiency of the scanning system. As these miscellaneous factors have been previously discussed hereinabove, modifications to the present procedure to improve its degree of accuracy will readily occur to those skilled in the art.

The geometrical optics model of FIG. 10J assumes that most bar code symbol surfaces behave as Lambertian radiators, wherein the process of irradiance from such surfaces (i.e. “diffusely reflective surfaces”) is goverened by Lambert's Law during laser beam scanning and light collection operations. In accordance with Lambert's Law, laser light diffusely reflected off the scanned code symbol is projected over an area having a circular collection aperture (i.e. A_(circular)). In order to calculate the Lambertian light collection efficiency E_(L) of each i-th facet, Lambert's Law requires that each facet have a circular geometry. In general, each facet on the scanning disc of the present invention has a non-circular geometry. To allow the use of the E_(L)-calculation procedure on such scanning disc, it is therefore necessary to first compute an effective circular aperture, A_(eff), for each i-th facet on the scanning disc under testing. This equivalent measure can be easily computed using the previously determined surface Area_(i) of the i-th facet and the well known circle-area formula (i.e. Area_(i)=πR²=A_(eff)), where R is defined as the radius of the effective circular aperture for the facet.

As shown in FIG. 10J, the Lambertian radiator model comprises a number of other geometrical parameters which factor into the calculation of E_(L) namely: Z, the distance from the point of code scanning to the effective circular aperture defined on the scanning disc; R_(pr), the radius of the projected effective circular aperture; B_(i), the diffraction angle of the outgoing laser beam from the i-th facet; and δ_(i), the half-angle subtended by the effective projected circular aperture. During the measurement stage of the procedure, physical measurements are made to determine Z_(i) (in inches), Area_(i) (in square inches) and B_(i) (radians) for each i-th facet. Compute A_(eff) using the formula A_(eff)=A_(i) Sin(B_(i)). Then R_(pr) is computed using the circle area formula: A_(eff)=πR_(pr)2. Then using computed R_(pr) and measured Z_(i), the half-angle δ_(i) for the i-th facet is computed using the expression: δ_(i)=a Tan[R_(pr)/Z_(i)], wherein atan =tan⁻¹. Having computed δ_(i), E_(L) can be calculated using the expression E_(L)=[sin(δ_(i))]² for small values of δ_(i) (i.e., less than 2 degrees). In FIG. 10L1, a numerical example is worked out for illustrative purposes.

Ideally, each facet should have equal Total Light Collection Efficiency which is defined as E H, for all values i. In most applications, one can expect the Total Light Collection Efficiency of the facets to deviate within an acceptable tolerance range, yet still consider such a scanning disc to have the total light collection efficiency of its holographic facets substantially “equalized” within the spirit of the present invention.

When the scanner designer determines that the scanning disc design satisfies its design criteria (e.g. equalized light collection efficiency among the facets, etc.), then the disc design process is completed and the facets of the scanning disc can be manufactured and thereafter assembled between the glass support plates of the disc. However, if the scanner designer cannot successfully layout the facets on the disc as described above, then as indicated at Block M in FIG. 11C, the designer may return to any of the stages in the scanner design process, and use the spreadsheet-based Scanline Production Model to recompute parameters based on newly assumed parameters in the scanner model. During this interactive design process, the scanner designer can perform “what-if” type analysis in order to arrive at a best or most suitable scanner design, given the set of system constraints presented to the designer.

DESIGNING A HOLOGRAPHIC LASER SCANNER HAVING CROSS-POLARIZING FILTERS BEFORE ITS PHOTODETECTORS

At this juncture it is appropriate to now describe how to design a holographic scanning disk for use in a holographic laser scanner employing light polarization filtering.

As shown in FIG. 10F, the S (or P) polarized laser beam produced from each VLD in the system is directed incident the scanning disk, sequentially diffracted by the rotating holographic facets, and then reflected off the beam folding mirrors towards a bar code symbol to be scanned within the scanning volume. As is well known, a portion of the S (or P) polarized laser beam incident on the code symbol is reflected off the glossy surface (i.e. substrate or overcoat) as an optical signal which retains the polarization state of the incident laser beam. The other portion of the polarized laser beam passes through the glossy coating, is intensity modulated and scattered (i.e. diffused) by the code symbol and reflects off the symbol as an unpolarized, intensity-modulated optical signal. A portion of these two signal components collectively travel back along the same optical path as the incident scanned laser beam and is diffracted by the corresponding facet towards the parabolic mirror. The parabolic mirror focuses the collected light rays of the reflected laser beam through the same facet with minimal light diffraction (i.e. off Bragg) through a P (or S) polarizing filter which attenuates (i.e. blocks) the S (or P) polarized component of the scan data signal while transmitting the P (or S) polarized component of the unpolarized component thereof to the photodetector for intensity detection. Advantageously, when using this scanning arrangement, the S (or P) polarized O-th diffractive order of the laser beam incident the facet is also blocked by he cross-polarizing filter, thus improving the SNR of the detected scan data signal in general. As shown in FIG. 10F, and as used hereinafter, the term S-cross polarizing filter shall mean a polarized light and block P polarized light, whereas the term P-cross polarizing filter shall mean a polarizing filter oriented on a photodetector so as to pass P polarized light and block S polarized light.

While the use of an S or P cross-polarizing filter effectively solves the problems associated with glare in the holographic scanning system described above, it does require a minor modification of the scanner design process of the present invention. In particular, the light diffraction efficiencies of the scanning facets must be modified from the way taught in Expressions No. 11 through 13 of FIG. 10C2 due to the fact that light of one polarization must be efficiently diffracted by the facets during scanning, while light of the orthogonal polarization must be efficiently diffracted by the holographic facet during light collection and detection. This condition is achieved by ensuring that the product of the outgoing S (or P) polarization diffraction efficiency of each facet and the return P (or S) polarization diffraction efficiency is maximized. Thus, the total out-and-back diffraction efficiency of each i-th facet, H_(i), is defined as the “product” of (i) the outgoing diffraction efficiency of the facet for the S (or P) polarization component of the incident laser beam and (ii) the return diffraction efficiency of the facet for the orthogonal P (or S) polarization of the laser beam.

When designing each facet on the scanning disc, all of the steps in the disc design method recited at Blocks A through F in FIG. 11A are carried out in the manner described above. The only modification to the scanner design method occurs at Block G of FIG. 11B when determining the holographic diffraction efficiency H_(i) for each facet. At this stage of the method, Expression No. 13 set forth in FIG. 10H2 is used to compute E_(t)[Δn_(i)], the total of out-and-back diffraction efficiency of each i-th facet, H_(i). As indicated by this mathematical expression, this parameter is defined as the product of the S and P light diffraction efficiencies, rather than the product of the S (or P) diffraction efficiency and the average of the S and P efficiencies, as shown in Expression 13 in FIG. 10C2, namely: E_(S)[Δn_(i)], the outgoing diffraction efficiency of the facet for the S polarization component of the incident laser beam; and E_(P)[Δn_(i)], the return diffraction efficiency of the facet for the orthogonal P polarization of the laser beam. These individual diffraction efficiency terms are provided by Expressions No. 11 and 12, respectively, in FIG. 10H2. As indicated in FIG. 10H2, component terms E_(S)[Δn_(i)] and E_(P)[Δn_(i)] and product term E_(t)[Δn_(i)] are graphically plotted as a function of modulation index Δn_(i) of the recording emulsion from which the i-th holographic facet is realized.

To practice the scanner design method of the present invention, this light diffraction efficiency expression (14) is inserted in the proper cells of the spreadsheet-based Scanline Production Model running on the HLD Workstation. While the S and P polarization diffraction efficiencies E_(S)[Δn_(i)] and E_(P)[Δn_(i)], and the total out-and-back diffraction efficiency for an S-polarized outgoing beam E_(t)[Δn_(i)] are plotted for facet Nos. 1 and 16 in FIGS. 10I1 and 10I2, respectively, for different values of modulation index Δn_(i), the spreadsheet based Model in practice uses the value of modulation index Δn_(i) which maximizes E_(t)[Δn_(i)] for the i-th facet. Once this value of Δn_(i) is found and the maximum E_(t)[n₁] computed for each i-th scanning facet, then the out-and-back diffraction efficiency of each i-th facet relative to facet No. 16 (i.e. the relative light diffraction efficiency, H_(i)) is computed for each i-th facet and stored along with the value of Δn_(i) used to compute this parameter value. This computation is carried out for each of the sixteen facets on the scanning disc under design. Then, the relative holographic diffraction efficiency H_(i) for each i-th facet is computed as the ratio of the product terms E_(t)[Δn_(i)]/E_(t)[Δn₁₆]. After carrying out this cycle of computations, a set of relative diffraction efficiencies {H_(i)} are obtained for the scanning disc that has been particularly designed for use with cross-polarization filters. Thereafter, the scanner designer returns to the spreadsheet-based Scanline Production Model to Block H and resumes the scanner design process described hereinabove until completion.

DESIGNING A HOLOGRAPHIC LASER SCANNING DISC HAVING FACETS WITH DIFFERENT FRINGE CONTRAST OVER THE BEAM SCANNING AND LIGHT COLLECTING PORTIONS THEREOF, FOR USE IN A HOLOGRAPHIC SCANNING SYSTEM WITH LIGHT POLARIZING FILTERS

In the above-described embodiment of the scanner design method hereof, cross-polarizers were used to eliminate the effects of glare during scanning. In the scanning disc design described above, the S and P diffraction efficiencies E_(S)[Δn_(i)] and E_(P)[Δn_(i)] were not both maximized, but rather the product of these terms, namely E_(t)[Δn_(i)], was maximized by finding the modulation index Δn_(i) at which this function “peaked” or attains its maximum value, assuming that the modulation index of the fringe structure throughout the i-th facet is uniform or the same over the entire facet. This fact is illustrated in the diffraction efficiency plots of FIG. 12. Notably, this design technique offers a compromise to the problem at hand by accepting the fact that the light diffraction efficiencies of the facets to S and P light do not attain maximum or peak values at the same value of modulation index, Δn_(i).

In the alternative disc design described hereinbelow, this constraint is removed from the design process, and instead of finding the single modulation index value for the emulsion at which the product of the diffraction efficiencies E_(S)[Δn_(i)] and E_(P)[Δn_(i)] are maximized, the alternative technique finds the modulation index value Δn_(i1) at which E_(S)[Δn_(i)] is maximized (e.g. peaked) and the modulation index value Δn_(i2) at which E_(P)[Δn_(i)] is maximized. Then during the facet manufacturing process, the i-th facet is selectively exposed to achieve portions with different light diffraction deficiencies, namely: the emulsion of the facet at the outer portion of the i-th facet along which the incident laser beam is incident is exposed by the Argon laser beam so that modulation depth Δn_(i1) is attained and thus light diffraction efficiency E_(S)[Δn_(i1)] maximized; and the emulsion of the facet at the inner portion of the i-th facet along which the rays of the return laser beam pass for collection is exposed by the construction laser beam (e.g. an Argon laser) so that modulation depth Δn_(i2) is attained and thus light diffraction efficiency E_(P)[Δn_(i1)] maximized. A scanning disc of such a design is shown in FIG. 12A. During this two-step exposure process, spatial masks are used to cover the regions of the i-th facet which are not to be exposed during the particular exposure process. By carrying out this facet design and construction technique, a scanning disc is produced having facets which optimize the diffraction efficiency of the S-polarization component of the laser beam incident the rotating scanning disc during scanning operation, while optimizing the diffraction of the P-polarization component of the laser beam reflected off a scanned symbol during light collecting operations.

As will be readily apparent, the use of a scanning disc having facets with regions made from emulsions (i.e. DCG) characterized by different depths of modulation, Δn_(i1) and Δn_(i2), will provide the holographic laser scanner of the present invention with a better overall light collection efficiency, as the inner light collecting portion of the facet does not have to be exposed to maximize the product of the efficiencies of the S and P polarizations, but rather exposed to maximize the efficiency for the polarization of the return light rays that are passed to the photodetector by the cross-polarizer thereon. This feature of the present invention will result in a significant improvement in the light collection efficiency of facets having large diffraction angles (or small B) (i.e. Nos. 4, 8, 12, and 16). The improvement which can be expected when using this technique is about 50% average improvement, which is the difference between using a 30 milliwatt laser beam over a 20 milliwatt laser beam, or a 40:1 SNR versus a 30:1 SNR. This provides a markedly improved performance when reading code symbols printed on glossy substrates or having glossy overcoats, as in many stock products.

As shown in FIGS. 12B1 through 12B3, a modified procedure is provided for designing a holographic laser scanner employing a scanning disc having dual modulation-depth or fringe-contrast regions over the beam sweeping and light collecting regions thereof. As shown, the steps of the method indicated at Blocks A though F and J through N in FIGS. 12B1 through 12B3 are substantially the same as in the method described in FIGS. 11A through 11C. The points of difference between the two alternative design methods begin at Block G in FIG. 12B2 where the spreadsheet-based Scanline Production Model running on the HSD workstation computes an “effective” relative light diffraction efficiency factor H_(effi) for each i-th split-design facet on the disc. The mathematical expression set forth in FIG. 12C is used to compute the parameter H_(effi) for each scanning facet. As indicated by this expression, a number of dependent parameters are involved in this calculation, including a number of area terms which must be initially assumed to perform the calculation. Other terms, such as the light diffraction efficiencies E_(S)[Δn_(i1)] and E_(P)[Δn_(i)] for each i-th facet can be computed using the expressions for light diffraction efficiency set forth in FIG. 10H2. The outer area of the i-th facet A_(outeri) can be assumed using knowledge of the laser beam diameter and the facet Rotation angle θ_(roti), Expression No. 17 in FIG. 8C2 of the facet, whereas the inner area of the facet A_(inneri) can be calculated by subtracting the inner area A_(inneri) from the total area of the facet, A_(totali). For purposes of the design method, the parameter A_(totali) is assumed to be the Area_(i) provided by the design method of FIGS. 11A through 11C.

After H_(effi) is calculated, the scanner designer proceeds to Block H and uses the spreadsheet-based Scanline Production Model to compute the light collection efficiency factor ζ_(i) for each facet. Then at Block I, the scanner designer uses the spreadsheet-based Scanline Production Model to compute the total light collection surface area of the facet, A_(totali). At Block I′, the scanner designer uses the spreadsheet-based Scanline Production Model to compare the assumed values of A′_(inneri) with computed values of A_(totali). Then based on the differences between these parameter values, the scanner designer returns to Block G in the design method, adjusts the assumed values for A′_(totali) and then repeats the steps indicated at Blocks G through I′, each time yielding a different value for H_(effi) required in the total area computation for the i-th scanning facet. When A′_(totali) converges upon A_(totali), then acceptable values for H_(effi) and A_(totali) have been found and the design process can then proceed to Block J and resume in the manner described in connection with FIGS. 11A through 11C. When an acceptable set of geometrical parameters have been obtained which satisfy the specified system constraints and performance criteria, the design process is completed and the scanner design can be constructed.

CONVERSION OF SCANNING DISC RECONSTRUCTION PARAMETERS

Typically, there is a great need to mass manufacture the holographic scanning disc in very large numbers. Thus, holographic mastering technique can be used. While any suitable mastering technique can be used, it will be necessary in the nearly all instances to holographically record the master facets at a recording λ_(C) which is different than its reconstruction wavelength λ_(R). The reason for this is generally well known: it is difficult to make holographic facets with high fringe-contrast at the reconstruction wavelength λ_(R), which in the illustrative embodiment is about 670 nanometers. Instead, it is easier to record the facets at a spectral wavelength at which high-contrast fringes can be realized and then play back at the wavelength of the VLDs in the scanner.

Presently, the preferred recording medium for recording facets with high-contrast fringes is Dichromated Gelatin (DCG) which exhibits its greatest sensitivity near 488 nm. Thus a blue laser beam is required during recording. In order to record the i-th HOE at its construction wavelength, and then reconstruct the same at another wavelength, it is necessary to translate (i.e. convert) its construction parameters {f_(i), A_(i), B_(i)} expressed at the reconstruction wavelength λ_(R), into a complete corresponding set of parameters expressed at the specified construction wavelength λ_(C). The process illustrated in FIGS. 28A1 through 28D can be used to carry out the necessary parameter conversions. In addition, non-symmetrical optical elements are introduced to eliminate, or minimize, aberrations produced by the wavelength shift between exposure and reconstruction using techniques well-known in the art. Thereafter, using the converted set of construction parameters, the HOE facets can be made using the converted set of construction parameters and the holographic recording system schematically represented in FIG. 13.

In FIGS. 28A1 and 28A2, a geometrical optics model is schematically presented for an incident laser beam being deflected by a facet holographic optical element (HOE), e.g. realized as a volume-type transmission hologram supported on the rotating scanning disc. As shown in FIG. 28A1, the incident laser beam enters the upper glass plate of the disc at incident angle θ(i.e. 90°−A_(i)) propagates through the upper glass plate, the gelatin, the lower glass plate, and then emerges therefrom at diffraction angle θ_(d)(i.e. 90°−B_(i)) towards its associated beam folding mirror. As indicated in FIG. 28A2, the laser beam being transmitted through the disc plates and gelatin of the holographic facet interacts with the high-contrast fringes recorded therein so that its direction of propagation is changed (i.e. modified) through the process of diffraction physics. As shown in these drawings, a number of parameters are required to construct a suitable geometrical optics model for this laser beam diffraction process, and the process by which the construction parameters are converted. In general, there are six input parameters to the conversion process and two output parameters. Three of the input parameters are derived from the scanning disk design process, namely: λ₁, the wavelength of the laser beam produced by the VLD during hologram reconstruction (i.e. laser beam scanning); the incident angle θ_(i,1)(i.e. 90°−A_(i)) at which the laser beam propagates through the facet (i.e. upper glass plate, the gelatin, the lower glass plate) during reconstruction (i.e. laser scanning); and the diffraction angle θ_(d.1) (i.e. 90°−B_(i)) at which the diffracted laser beam emerges from the facet and propagates towards to its associated beam folding mirror. The other three input parameters provided to the parameter conversion process are derived from the HOE construction technique used to fabricate the holographic facets, namely; ζ₂, the wavelength of the laser beam used during HOE construction; n₀, the average (i.e. bulk) index of refraction of the recording medium before fringe development processing; and n₂, the average index of refraction of the recording medium after fringe development processing.

As set forth in the table of FIG. 28AD, the conversion process produces two output parameters, namely: θ_(i.2), the Angle of Incidence (Reference Beam Angle) θ_(R) for the second (construction) wavelength λ_(C), and θ_(d.2), the Angle of Diffraction (Object Beam Angle) θ_(O) for the second (construction ) wavelength λ_(C), both defined in FIG. 13. These two parameters and the aberration correcting optics are used to configure the HOE recording system shown in FIG. 13. All other parameters comprising the process model are intermediate parameters inasmuch as they establish relationships between the input and output parameters of the conversion process. In FIGS. 28, 28C1 and 28C2, these intermediate parameters are defined as follows: the incident angle α₁ inside the medium after development processing; the incident angle β₁ inside the medium after processing; d, the surface inter-fringe spacing of the recorded fringes; φ, the tilt angle of the Bragg Planes; θ_(0.1), the Angle relative to the Bragg planes; L, the separation of the Bragg planes, determined by the Bragg condition equation; θ_(0.2), the Angle relative to the Bragg planes for the second (i.e. construction) wavelength satisfying the Bragg condition, before fringe development processing; α₂, the Angle of Incidence inside the recording medium for the second wavelength, before fringe developing processing; and β₂, the Angle of Diffraction inside the recording medium for the second wavelength, before fringe developing processing.

Using the input parameters defined above, the output parameters θ_(1.2)=θ_(O) and θ_(d.2)=θ_(R) can be readily computed using Equations No. 10 and 11 set forth in FIGS. 28C1 and 28C2. These two computed parameters, along with the previously determined index modulation Δn_(i) and the aberration correcting optics can be collectively used to construct the i-th facet of the designed scanning disc using a laser beam having wavelength λ_(C) and a recording medium having average indices of refraction n₀ and n₂ before and after fringe structure development, respectively. In the illustrative embodiment, the preferred recording medium is dichromated gelatin (DCG) having its maximum light sensitivity in the blue spectral range, and thus the necessary construction wavelength for exposing this recording medium can be produced by an Argon gas laser with a peak spectral output centered at about 488 nanometers. For each designed facet, a set of construction parameters are determined using the above-described method and thereafter used to physically construct a “master” facet at the second (construction) wavelength λ_(c). The master facet can then be used to make one or more facet “copies” for mass production of the holographic scanning disk.

CONSTRUCTING HOLOGRAPHIC LASER SCANNING DISC USING WAVELENGTH-CONVERTED CONSTRUCTION PARAMETERS

As shown in FIG. 13, each holographic facet is made by producing a reference laser beam from a laser source. By passing the reference laser beam through a beam splitter, an object laser beam is produced in a conventional manner and using anamorphic optics, an object beam is formed having beam characteristics which are specified by parameters f_(i) and θ_(ri). Then as shown, both the reference beam and the object beam are directed incident upon a holographic recording medium (e.g. DCG) supported upon a substrate. The angle of incidence for the reference beam is specified by parameter θ_(i2), whereas the angle of incidence for the object beam is specified by the parameter θ_(d2), as shown. The geometrical configuration of this recording system is shown in FIG. 13 with all of the holographic facet recording parameters illustrated.

POST MANUFACTURE PARAMETER VERIFICATION

After constructing a holographic scanning disc in accordance with the teachings herein disclosed, it will be desired in many applications to verify that such scanning discs in fact embody the various features of the present invention. Inasmuch as the particular value of modulation index required for each facet is controlled by controlling laser power and gelatin quality during facet exposure, there is a degree of variability in facet light collection efficiency which can be expected in manufactured scanning discs. Also, inasmuch as it is impossible to maintain a perfect degree of uniformity in thickness in the emulsion layer of each facet during recording (i.e. exposure) operations, it can also be expected that the light collection efficiency of each facet may deviate slightly from its value determined during the disc design process. Consequently, there is a need during scanning disc manufacture to maintain accurate control over (i) the specified index modulation for each of the facets, as well as (ii) the uniformity of the emulsion layers of each of the facets. In order to maintain high quality control during the disc manufacturing process, it will be important to verify that the light collection efficiencies of the facets on each manufactured scanning disc are substantially equal in value, thereby allowing the use of low band-width photodetection and signal processing circuitry. The tool for computing Lambertian light collection efficiency, E_(L), illustrated in FIGS. 10J through 10L and described above, can be used to determine that the Total Light Collection Efficiency (i.e. E_(Li)H_(i)) of each facet on a manufactured scanning disc is substantially equal, as desired in nearly all holographic scanning applications.

LASER BEAM PRODUCTION MODULE OF THE FIRST ILLUSTRATIVE EMBODIMENT

Having described the overall system architecture of the scanner of the present invention and how to design and manufacture scanning disks for use in the same, it is appropriate at this juncture to now describe in great detail several different embodiments of the laser beam production module of the present invention, as well as different methods of designing and constructing the same.

In FIG. 14, the laser beam production module of the first illustrative embodiment is shown installed within the holographic laser scanner of the present invention using a parabolic light collecting mirror disposed beneath the scanning disc at each scanning station provided therein. In FIG. 14A, the ray optics of such a scanning system are schematically illustrated. Notably, the laser beam production module has several functions. The module should produce a circularized laser beam that is directed at point r_(o) on the rotating scanning disk, at the prespecified angle of incidence θ_(i) (i.e. 90°−A_(i)), which, in the illustrative embodiment, is precisely the same for all facets thereon. Also, the module should produce a laser beam that is free of VLD-related astigmatism, and exhibits minimum dispersion when diffracted by the scanning disk.

In the first illustrative embodiment shown in FIGS. 15A through 15K, the module 13A comprises an optical bench 60 having several adjustable mechanisms for mounting components such as a VLD 53A (53B, 53C), an aspheric collimating lens 61, a prism 62, a mirror 63 and a light diffractive grating 64 having a fixed spatial frequency. These components are configured in such a manner so as to achieve the objects of the present invention. Prior to describing how to make and assemble the components of this module, it will be helpful to first describe the general structure of each of these basic components, including the adjustable mounting mechanisms provided by the optical bench thereof.

As shown in FIG. 15, the laser beam production module of the first illustrative embodiment is mounted beneath the edge of the parabolic light focusing mirror, and below the associated beam folding mirror. As shown in FIG. 15A, the optical bench of the module comprises a point plate with a rotatable platform for mounting the prism and an adjustable subassembly for mounting the VLD and aspheric collimating lens as an integrated subassembly. The geometrical characteristics of prism 62 are illustrated in FIGS. 15I1 and 15I2, whereas the geometrical characteristics of mirror 63 and HOE plate 64 are shown in FIGS. 15J and 15K, respectively. As will become apparent hereinafter, the function of these adjustable platforms is to allow geometrical parameters defined among the optical components to be configured in a manner that results in a beam circularization, astigmatism elimination, and beam dispersion minimization. The optical bench of the beam production module is mounted relative to the optical bench of the scanning system so that the produced laser beam is directed incident the scanning disk, at angle A_(i) defined hereinabove.

As shown in greater detail in FIG. 15B, each module bench comprises a base portion 65, and an integrally formed grating/mirror support portion 66. As shown in FIG. 15C, the grating/mirror support portion 66 is disposed at an obtuse angle relative to the base portion so that the light diffractive grating 64 will be automatically oriented with respect to the scanning disc at a prespecified angle (determined during the module design method hereof) when the module bench 60 is mounted on scanner bench 5, such alignment is achieved by way of pins 67 on the scanner bench 5 receiving alignment holes 68 formed in the underside of module bench 60, as shown in FIGS. 15 and 15A. The grating/mirror support portion 66 includes a side support surface 69 for supporting the planar mirror 63, and also a top support surface 70 for supporting the light diffractive grating (i.e. HOE plate). Grooves can be formed along these support surfaces in order to securely retain the mirror and the HOE plate.

As shown in FIG. 15B, the base portion also has a recess 71 within which pivot plate 72 is pivotally mounted from pivot point 72, identified in FIG. 15B. As shown in FIGS. 15E1 and 15E2, pivot plate 72 has a first portion 72A upon which a cylindrical platform 73 is rotatably mounted, and a second portion 72B upon which VLD and aspheric lens mounting assembly is fixedly mounted. The function of cylindrical platform 73 is to provide a mounting surface for the prism. Any suitable adhesive can be used to secure the prism upon the top surface of platform 73. An adjustment screw can be provided adjacent to the platform so that the cylindrical disk can be secured in position when adjustment of the prism has been completed.

Subcomponents comprising the VLD and collimating lens mounting assembly are shown in FIGS. 15E1 through 15H2. As shown in FIGS. 15F1 and 15F2, a VLD mounting yoke 75 is provided for pivotally supporting an optics telescopic assembly comprising the VLD block 76 shown in FIGS. 15G1 and 15G2, and the lens barrel 77 shown in FIGS. 15H1 and 15H2. The function of the VLD block 76 is to securely mount the VLD at one end thereof. The function of lens barrel 77 is to securely retain the aspheric collimating lens 61. A spring is located between the VLD housing and lens barrel for producing a resistive force against the threading action of the lens barrel while adjusting the VLD-to-lens distance parameter. Also, this spring functions to compensate for tolerances in the fit between the lens barrel and VLD block. This feature permits precise adjustment of d while using inexpensive, easy to manufacture components in mass production applications. The lens barrel and lens together are mounted within the other end of the VLD block, as shown. Threads 77A are provided on the exterior surface of the lens barrel, while matching threads 76A are provided on the interior surface of the bore 76B extending through the VLD block 76. The pin hole 75A in the base of VLD yoke 75 pivots about pin 73C on the pivot plate. This arrangement allows the position of the aspheric collimating lens to be adjusted relative to the fixed position of the VLD, during a configuration procedure to be described in great detail hereinbelow. A spring 81 is inserted into the end of bore 76B which produces a resistive force against the lens barrel as it is threaded into the bore. When the VLD yoke, VLD, lens barrel and aspheric collimating lens are assembled together as a single adjustable subassembly, then the adjustable unit is pivotally supported in a gimbal like manner within the yoke by way of support pins 78A and 78B, shown in FIG. 15G1 which pass through bores 79A and 79B in yoke 75 and screw into thread holes 80A and 80B, respectively, in the VLD Block 76. This arrangement allows the direction of the laser beam from the lens barrel to be adjusted in the up and down direction, relative to the face of the prism and thus the planar mirror. Also, the pivotal mounting of the yoke relative to the base plate, permits the orientation of the yoke, and thus the direction of the laser beam, to be pivotally adjusted relative to the face of the prism during the configuration procedure. Additionally, the pivotal mounting of the pivotal base plate within the recess of the module optical bench allows the direction of the circularized beam emerging from the prism to be adjusted relative to the planar mirror. As will become apparent below, this adjustment mechanism permits the scanner designer to properly configure the components of the VLD so that the above objectives are satisfied in accordance with the principles of the present invention.

As shown in FIG. 16, there are three basic steps involved in the design of a laser beam production module according to the teachings of the present invention.

As indicated at Block A in FIG. 16, the first step of the module design method involves designing a first optical system comprising the i-th facet and the fixed spatial frequency diffraction grating within the laser beam production module. The sole function of this optical system is to substantially eliminate laser beam dispersion during the diffraction of the incident laser beam through the rotating scanning disc. In the first illustrative embodiment, the first optical system comprises fixed spatial-frequency diffraction grating (i.e. plate) 64 and the i-th facet previously designed using the disc design method of the present invention. As indicated at Block B, the second step of the method involves designing a second optical system comprising the VLD 53A, aspheric collimating lens 61 and prism 62, configured so as to circularize the laser beam produced from the VLD and eliminate astigmatism in the circularized beam beyond the prism. The third and final step is to couple the first and second optical systems by way of planar mirror 63 so as to form the laser beam production module of the first illustrative embodiment, shown in FIGS. 15A through 15K. Thereafter, the module can be parametrically configured and installed within the holographic laser scanner. The details of this process will be described hereinbelow.

In FIG. 17A, the problem of beam dispersion during laser beam diffraction through the scanning disc hereof is schematically illustrated. The parameters used to construct the geometrical optics model of the beam diffraction process are shown in FIG. 17B. The relationship between the grating parameters and the diffraction angle and the diffraction angle and the wavelength of the spectral components of the laser beam are defined in FIG. 17C. The graphical plot of diffraction angle versus wavelength shown in FIG. 17D explains why an incident laser beam produced from a conventional VLD tends to disperse as it is diffracted across the scanning facet. The various spectral components associated with the VLD beam, due to superluminescence, multi-mode oscillation and mode hopping, exit the HOE facet on the scanning disc at different diffraction angles dependent on the wavelength thereof. The wavelength dependency of the diffraction angle is illustrated in 17D.

In order to minimize wavelength-dependent dispersion at each facet along the scanning disc of the present invention over the wavelength range of concern (e.g. 600 to 720 nanometers), the diffraction grating in the first optical system described above is positioned at a tilt angle ρ, defined as shown in FIG. 18A. The mathematical expression describing the relationship between the incidence angle θ_(i1), the diffraction angle θ_(dc1) at the reconstruction wavelength, the wavelength of the incident beam λ_(c) and the grating spacing d₁ is described by Expression No. 1 in FIG. 18C. This equation is simply the grating equation which describes the behavior of fixed frequency diffraction gratings, such as the compensation plate 63 used in the first optical system. Then using algebraic techniques upon Expression No. 1, an expression for θ_(d1)(λ) can be derived as provided by Expression No. 3 in FIG. 18C. The relationship between the angle of diffraction of the diffraction grating θ_(dc1), the angle of incidence at the i-th facet θ_(i2) and the tilt angle ρ is described by Expression No. 2 in FIG. 18C. This mathematical expression is derived using a number of well known trigonometric relations. While each HOE facet on the designed scanning disc has a variable frequency fringe structure in order to realize its focal length f_(i), the design procedure models each facet as if it were a fixed frequency grating. This assumption can be made without introducing significant error in the design as the goal of the first optical system is to minimize the beam dispersion through the HOE facets over the range of diffraction angles for which the facets have been previously designed to produce the prespecified scanning pattern. In the illustrative embodiment, the range of diffraction angles is from about 26.6° to about 47.5°, with the average diffraction angle being about 37 degrees. Thus this average diffraction angle 37° will be selected as the diffraction angle used to design the first optical system. This diffraction angle is indicated by θ_(dc2) in the geometrical optics model, and describes the average direction in which the diffracted laser beam is directed towards the beam folding mirrors in the scanning system. Using the above assumption about each HOE facet on the scanning disc allows the facet in the first optical system to be modelled by the well known diffraction equation, expressed in the form of Equation No. 3 set forth in FIG. 18C.

In order to complete the design of the first optical system, it is necessary to find a set of values for the parameters representing the first optical system which results in minimizing the deviation of the average diffraction angle θ_(d2) over the range of spectral wavelengths that can be expected to be produced from a conventional VLD used to construct the designed laser beam production module. Ideally, the deviation is zero over the wavelength range of interest; however, this is not achievable in practice. Instead, this deviation is minimized over the wavelength range of interest. Finding the set of parameters that will achieve this objective can be achieved by the following procedure.

Using Expression No. 3 in FIG. 18C, the system designer selects the value of incidence angle θ_(i1) required by scanner height and width dimension constraints, and thereafter evaluates Expression No. 3 for the range of wavelength values λ of interest. During this evaluation step, an initial value for the tilt angle ρ is selected, whereas parameters θ_(i2,) d₂ and λ_(R) indicated in Expression No. 3 are known or derivable from the previous disc design process. In particular, d₂ is arrived at by selecting the average fringe spacing among the numerous variable frequency holographic facets realized on the previously design scanning disc. For a large number of different wavelength values within the λ range, the diffraction angle θ_(d2) is then calculated so that the θ_(d2)(λ) can be plotted as a function of wavelength λ, as shown in FIG. 18D. From this plot, the deviation can be determined if it is not acceptable, then the above process is repeated using a different tilt angle ρ until the plot θ_(d2)(λ) has an acceptable deviation over the wavelength range of interest. After several interactions, an acceptable parameter value for tilt angle ρ will be found. At this stage of the design process, the incidence angle parameter θ_(i1), the construction angle of diffraction θ_(dc1) and the specified nominal reconstruction wavelength λ_(R) provide a set of parameters sufficient to construct the diffraction grating (i.e. wavelength compensation plate) while the tilt angle ρ is sufficient to mount the diffraction grating relative to incidence point r₀ on the scanning disc so that beam dispersion is minimized over the range of spectral wavelengths produced by the VLD during beam scanning operations. A set of parameters found to minimize beam dispersion over the output bandwidth of the VLD are set forth in FIG. 18B1. These parameters are based on the disc design parameters for the scanning disc and scanning pattern of the illustrative embodiment. As shown in FIG. 18D, these parameters result in diffraction angles θ_(d2) which are substantially the same for various spectral components within the output bandwidth of the VLD. In practical terms, this means that each of these spectral components in the incident circularized laser beam will be diffracted at substantially the same angle from the scanning disc, minimizing the dispersion of the diffracted scanning beam.

Notably, the above-described method of designing the first optical system of the laser beam production module provides the system designer with two degrees of design freedom as either the incidence angle θ_(i1) or the tilt angle ρ can be used as a design variable while the other is used as a design constraint. This inventive feature allows the angle of incidence θ_(i1) to be markedly different from angle of diffraction θ_(d2), while nevertheless minimizing beam dispersion through the scanning disc over the spectral bandwidth of the laser beam produced from the VLD. The design method permits the incidence angle θ_(i1) to be any one of a large range of values which allows the constructed laser beam production module to be physically mounted on the system optical bench between the optical bench and the scanning disc, within the width dimension constraints of the scanner housing. The design method also permits the tilt angle ρ to be any one of a large range of values which provides the designed great flexibility in mounting the laser beam production module relative to the scanning disc and parabolic light collecting mirror disposed therebeneath. These features of the present invention assist the system designer in designing and constructing a holographic laser scanner having a scanner housing volume which has been minimized in relation to its specified scanning volume.

Having designed the diffraction grating employed in the first optical system of the laser beam production module, it is appropriate to briefly address the construction of the same. Typically, there will be a great need to mass manufacture laser beam production modules embodying “wavelength-compensation” diffraction gratings, of the type described above. Thus, holographic mastering techniques are ideally used. While any suitable mastering technique can be used, it will be necessary in nearly all instances to holographically record the master diffraction gratings at a recording wavelength λ_(C) which is different than its reconstruction wavelength λ_(R). The reason for this is generally well known: it is difficult to make holographic gratings with high fringe-contrast at the reconstruction wavelength λ_(R), which in the illustrative embodiment is about 670 nanometers. Instead, it is easier to record the gratings at a spectral wavelength at which high-contrast fringes can be realized and then playback at the wavelength of the VLDs in the scanner. Presently, the preferred recording medium for recording diffraction gratings with high-contrast fringes is Dichromated Gelatin (DCG)) which exhibits its greatest sensitivity near 480 nm. Thus, a blue laser beam is required during recording. In order to record the diffraction grating at its construction wavelength, and then reconstruct the same at another wavelength, it is necessary to translate (i.e. convert) its complete set of construction parameters {θ_(i1), θ_(dc1)} expressed at the reconstruction wavelength λ_(R), into a complete corresponding set of parameters expressed at the specified construction wavelength λ_(C). The process illustrated in FIG. 19A through 19E is virtually identical to the process shown in FIGS. 28A1 through 28D and can be used to carry out the necessary parameter conversions. Details regarding the process of 19A through 19E can be found by referring to the description of the process of FIGS. 28A1 through 28D detailed above. Thereafter, using the converted set of construction parameters, the holographic diffraction gratings can be made using the converted set of construction parameters and the holographic recording system schematically represented in FIG. 19F.

In the illustrative embodiment, the preferred recording medium for the diffraction grating of the laser beam production module is DCG having its maximum light sensitivity in the blue spectral range, and thus the necessary construction wavelength for exposing this recording medium can be produced by an Argon gas laser with a peak spectral output centered at about 488 nanometers. The set of construction parameters determined using the above-described conversion method can be used to physically construct a “master” diffraction grating at the second (construction) wavelength λ_(c), and then one or more grating “copies” can be made from the master diffraction grating for mass production of the laser beam production modules.

After completing the design of the first optical system of the laser beam production module, the second step of the design method involves designing the second optical system thereof. As mentioned above, the function of the second optical system comprising the VLD, aspheric collimating lens and the beam circularizing prism, is to circularize the laser beam produced from the VLD and completely eliminate astigmatism along the circularized beam from a point beyond the second surface of the beam expanding prism. In order to design such an optical system, the present invention teaches geometrically modelling the production of the laser beam from a semicondictor VLD, while describing the phenomenon of astigmatism inherently introduced along the produced laser beam. This novel modelling technique will be described in detail below.

In FIG. 20, a geometrical model is provided for a semiconductor VLD which produces a laser beam having astigmatism inherently introduced along the laser beam. In general, it is well known that the laser beam produced from conventional VLDs has two different beam components, namely: a first beam component having a very narrow dimension which is parallel to the width dimension of the VLD junction (i.e. resonant cavity); and a second beam component having a very wide dimension which is parallel to the height of the VLD junction. For purposes of exposition, the first beam component shall be referred to as the “P external wavefront” of the produced laser beam, whereas the second beam component shall be referred to as the “S external wavefront” of the produced laser beam. These designations S and P refer to conceptual cylindrical wavefronts which spread in a direction perpendicular (S) or parallel (P) to the VLD junction and are not to be confused with the S wave-polarization and the P wave-polarization directions of the incident laser beam at the scanning disk surface, defined hereinabove. As illustrated in FIG. 20, the “S external wavefront” of the produced laser beam is deemed to originate from an “effective S source” located within the volumetric extent of the VLD junction, whereas the “P external wavefront” of the produced laser beam is deemed to originate from an “effective P source” located within the volumetric extent of the VLD junction. Inasmuch as the “effective P source” is spatially separated from the “effective S source” by some distance δ, referred to as the “astigmatic difference” inherent in each VLD and statistically varying from VLD to VLD, the geometrical model predicts that the “S external wavefront” will diverge at a rate different than the “P external wavefront” along the produced laser beam and therefore the laser beam will exhibit astigmatism in the well understood sense. According to this geometrical model, nearly all of the power of these external wavefront components reside in the Electric Field vector of these electromagnetic wavefronts and the polarization thereof is parallel to the width dimension of the VLD junction, which is commonly referred to as “transverse electric” polarization, or the TE mode of oscillation of the VLD. According to the model, the S point source produces a cylindrical wavefront whose center of curvature is located at the S source, whereas the P point source produces a cylindrical wavefront whose center of curvature is located at the P source. Details concerning the physics of VLDs can be found in “Heterostructure Lasers ” Parts A and B by H. C. Casey, Jr. and M. B. Panish, Academic Press 1978. Notwithstanding this fact of VLD physics, it is important to understand that the “effective S source” and the “effective P source” are constructions of the geometrical model which have been developed for the purpose of designing the second optical system of the laser beam production module of the present invention in accordance with the objects of the present invention. While there may be structural correspondence between the “effective S source” and junction geometry and between “effective P source” and junction geometry, there is no need to specify such correspondences herein for purposes of the present invention. What is important to practicing this aspect of the present invention is to employ this novel geometrical model of the VLD in order to design the second optical system as will be described hereinbelow. The advantage in doing so will become apparent hereinafter.

The method of designing the second optical system proceeds by modelling the VLD with geometrical model of FIG. 20 in relation to a geometrical optics model of the aspheric collimating lens and the beam circularizing prism, as shown in FIG. 20A. In FIGS. 20B1, 20B2 and 20B3, the geometrical optics model of the second system of the laser beam production module is shown in greater detail. In particular, these figure drawings graphically illustrate the geometrical and optical parameters used to construct the geometrical optics model of the second system, namely: the location of the effective sources of the S and P wavefronts associated with the VLD; δ, the astigmatic difference of the VLD, defined as distance between the effective sources of the S and P wavefronts; f₁, the focal length of the aspheric collimating lens; d, the distance between the focal point of the aspheric collimating lens and the S wavefront (i.e. Beam) source; D₁, the diameter of the P wavefront (i.e. Beam) leaving the aspheric collimating lens; D₂, the expanded diameter of the P wavefront leaving the prism; M, the beam expansion factor characteristic of the beam expanding prism, defined as D₂/D₁/D_(i); n, the refractive index of the prism material; θ_(Pi1), the angle of incidence of the lower portion of the converging P beam at the face of the prism; θ_(Pi2), the angle of incidence of the upper portion of the converging P beam at the face of the prism; φ_(P1), the angle of convergence of the P beam leaving the aspheric collimating lens; φ_(S1), the angle of convergence of the S beam leaving the aspheric collimating lens; φ_(P2), the angle of convergence of the P beam leaving the prism; φ_(S2)=φ_(S1), the angle of convergence of the S beam leaving the prism; L_(P1), the image distance for the P source imaged by the aspheric collimating lens; L_(P2), the image distance for the P source after inserting the beam expanding prism; L_(S1), the image distance for the S source imaged by the aspheric collimating lens; L_(S2)=L_(S1), the image distance for the S source after inserting the beam expanding prism; θ_(Pr1), the angle of refraction of the lower portion of the converging P beam in the prism; θ_(Pr1), the angle of refraction of the upper portion of the converging P beam in the prism; α, the prism apex angle which equals θ_(Pr1) by design for sake of convenience; θ_(Pi3)=θ_(Pr1)−θ_(Pr2)=α−θ_(Pr2), the angle of incidence of the upper portion of the converging P beam at the second surface of the prism; and θ_(Pr3)=φ_(P2) the angle of refraction of the upper portion of the converging P beam leaving the second surface of the prism. Collectively, these parameters constitute the geometrical optics model of the second optical system. Notably, the distance between the first surface of the prism and the principal plane of the collimating lens need not be considered as a parameter to the model provided that the entire cross-sectional diameter of the beam is incident (i.e. falls) upon the first surface of the prism, which is a very easy assumption to satisfy in practice.

In FIG. 20C1, a set of assumed values are presented for various parameters in the model which can remain fixed during the design process. In FIG. 20D, a set of equations are provided which define particular relationships between certain parameters in the geometrical optics model of the second optical system. The MATHCAD tool available within the HSD Workstation of the present invention can be used to realize the geometrical optics model of the second optical system. As clearly illustrated, Expressions No. 1 to 13 in FIG. 20D lead to the derivation of expressions for L_(P2) and L_(S2), the distances of the image of the P source and the image of the S source after being imaged through the aspheric collimating lens and the beam expanding prism. From these functions, the curvature of the S cylindrical wavefront as it immediately emerges from the second surface of the prism can be defined as 1/L_(P1), whereas the curvature of the P cylindrical wavefront as it immediately emerges from the second surface of the prism can be defined as 1/L_(P2). Expressed in other words, the radius of curvature of the S cylindrical wavefront as it immediately leaves the second surface of the prism is given by 1/L_(S2), whereas the radius of curvature of the P cylindrical wavefront as it immediately leaves the second surface of the prism is given by 1/L_(P2).

It is well known that each VLD having a non-zero astigmatic difference, defined herein as δ, will produce a laser beam which exhibits astigmatic properties. However, it has been discovered that, for each non-zero value of δ and assumed values of incidence angles θ_(Pi1) and θ_(Pi2), there exists a realizable value of d, at which the S and P cylindrical wavefronts leaving the second surface of the prism have equal radii of curvature, as indicated in the plot shown in FIG. 20E. Under such optical conditions, both the S and P cylindrical wavefronts emerging from the second surface of the prism are converging along the outgoing optical axis of the prism at the same rate (by virtue of their equal radii of curvature) and the resulting wavefront is spherical and free of astigmatic aberrations associated with the non-zero inherent astigmatic difference in the VLD. Through rigorous quantitative analysis, it has also been discovered that small changes in the angles of incidence θ_(Pi1) and θ_(Pi2) have a significant effect in altering the radius of curvature of only one of the cylindrical wavefronts (P wavefront) while minimally affecting the radius of curvature of the P wavefront. Notably, this condition exists because in the geometrical optics model of the VLD, the P-source resides further away from the principal plane of the aspheric collimating lens than does the S-source. Consequently, the mathematical structure of the geometrical model for the second optical system suggests that parameters d, θ_(Pi1) and θ_(Pi2) be selected as “adjustable parameters” used during the parameter adjustment procedure hereof so that the above-described optical conditions are satisfied and the astigmatism eliminated.

In view of these discoveries, it will be helpful to briefly discuss the optical function that each of the components performs in the second optical system when its parameters are configured in the astigmatism-elimination case described above. Firstly, as stated above, the S and P sources represented within the VLD produce cylindrical wavefronts emanating from the location of these S and P sources, respectively. The function of the aspheric collimating lens is to pass the S and P wavefronts, while changing the radius of curvature for both of these wavefronts, as well as their apparent center of curvature. Notably, in the second optical system, both the S and P wavefronts are assumed to propagate on axis, and therefore off-axis aberrations will be negligible and thus need not be considered. The function of the prism is to significantly change the radius of curvature of only one of these cylindrical wavefronts, while minimally changing the radius of curvature of the other cylindrical wavefront. This significant degree of change in the radius of curvature is a strong function of the angles of incidence θ_(Pi1) and θ_(Pi2) measured with respect to the first surface of the prism. This functional relationship and the manner in which such dependency is established among the various parameters in the Mathcad model, can be readily seen by carefully examining Expressions No. 2 through 13 set forth in FIG. 20D. Most importantly, the above analysis reveals that the design method of the present invention provides the designer with two degrees of freedom when finding the set of parameters that satisfies the optical condition illustrated in the plot shown in FIG. 20E. In particular, the scanner designer may select a given value for the prism incidence angles θ_(Pi1) and θ_(Pi2) (i.e. the prism tilt angle θ_(Prism-tilt)), and then find the parameter value for d (i.e., the distance from the focal length of the collimating lens to the S source), which eliminates astigmatism at the second surface of the prism. Alternatively, the scanner designer may select a given value for the distance d, (i.e., by setting the VLD-to-lens separation D to an initial value) and then find the parameter values for the prism tilt angle θ_(Prism-tilt) which eliminates astigmatism at the second surface of the prism. This is a very important fact inasmuch as it will be desirable in many applications to control the ellipticity (i.e. aspect ratio) of the spherical converging wavefront produced from the second surface of the prism. With this degree of freedom available in the second optical system of the present invention, the ellipticity of the spherical wavefront from the second surface of the prism can be easily controlled by selecting the appropriate prism incidence angles θ_(Pi1) and θ_(Pi2). This feature of the present invention is of great value in many scanning applications. In particular, when scanning dot-matrix codes on poorly printed codes, it will be desirable to produce laser beams having an aspect-ratio so that the beam height is greater than the voids present between code elements (e.g. bars). The use of such laser beams has the effect of averaging out such voids and thereby improves the first-pass read rate of such codes.

In any particular design application, the approach that will be used will depend on, for example, the physical constraints presented by the holographic scanner design. In order to find the distance d or prism tilt angle θ_(Prism-tilt) at which the optical condition of FIG. 20E is achieved, two different parameter adjustment procedures have been developed. As will be described in greater detail below, these techniques are based on the mathematical structure of the model used to find the conditions at which astigmatism is eliminated while the elliptically shaped laser beam is circularized while passing through the prism of the second optical system of the laser beam production module of the first illustrative embodiment.

In practice, it is not feasible to empirically measure the astigmatic difference δ for each VLD to be used in the construction of a laser beam production module. Consequently, it is not feasible to use Expressions 14 and 15 in FIG. 20D to compute the distance d for selected values of incidence angles θ_(Pi1) and θ_(Pi2) using the mathematical expressions for the S and P source image distances. Instead, the approach adopted by the design method of the present invention is to exploit the two degrees of freedom in the geometrical model of the second optical system and provide two different procedures which may be used to adjust (i.e. configure) the parameters of the system to eliminate astigmatism, circularize the laser beam, and optionally to adjust the focal point of the spherical converging wavefront (i.e. the resulting beam) emerging from the second surface of the prism. To avoid obfuscation of the present invention, these two techniques will be first described in general terms, with explanation of how the various steps in the procedures affect geometrical properties of the S and P cylindrical wavefronts, as well as the resulting spherical wavefront produced from the second surface of the prism. Thereafter, two illustrative embodiments of these parameter adjustment techniques will be described with reference to the parameter adjustment system according to the present invention shown in FIG. 21A, which can be used to adjust the geometrical and optical parameters of assembled laser beam production modules so that the various objects of the present invention are achieved therein.

In general, the function of the parameter adjustment system 85 of FIG. 21A is to allow the prism tilt angle, θ_(Prism-Tilt) and distance d, to be adjusted during the assembly/alignment procedure so that an astigmatism-free laser beam with a desired aspect-ratio is produced. Notably, by definition of parameter d in FIG. 20A, adjustment thereto can be achieved by simply adjusting the VLD-to-lens separation D. As shown, the parameter adjustment system 85 comprises an optical bench 86 upon which a pivot plate mounting fixture 87 is stationarily mounted. The function of the pivot plate mounting fixture is to mount during the parameter alignment procedure, pivot plate 72 carrying an optical subassembly comprising the VLD, the barrel, the lens mount, and the yoke. A beam scanning device 88, such as Model No. 1180-GP from Photon, Inc., is mounted on the optical bench of the parameter adjustment system along a first optical axis 89 which passes through test focusing lens 90, the optical axis of the second surface of the prism when the prism platform 73 with the prism thereon is mounted within second recess in the pivot plate. Also, a beam detector (e.g. quadrant detector) 91 is mounted on the optical bench along an optical axis 92 which passes through the center of the first surface of the prism when the prism platform with the prism thereon is mounted within the second recess in the pivot plate.

As indicated at Block A in FIG. 21B, the first step of the first generalized parameter adjustment technique involves selecting values for all parameters in the geometrical optics model for the second optical system except for the distance d and the incidence angles θ_(Pi1) and θ_(Pi2) (i.e. prism tilt angle θ_(Prism-tilt)), which are treated as variables in the process. As indicated at Block B, the second step involves selecting initial values for parameters d and θ prism-tilt which can be accomplished by virtually any criteria (θ_(prism-tilt)). Then as indicated at Block C in FIG. 21B, the procedure involves setting the incidence angles θ_(Pi1) and θ_(Pi2) so that a desired beam ellipticity (i.e. aspect ratio) is achieved on the second surface of the prism. In the event that a circular beam cross-section is desired at the second surface of the prism, and as well along the scanning beam, the aspect ratio will be unity, whereas when an elliptical beam cross-section is desired the aspect ratio will be some value not equal to unity. In essence, this step presents a parameter constraint which the second system must satisfy.

As indicated at Block D in FIG. 21B, the VLD-to-lens separation D is adjusted so as to find the parameter value d at which the radius of curvature of both the S and P cylindrical wavefronts are made equal at the second surface of the prism, resulting in a spherical wavefront thereat which is converging along the optical axis of the second optical system. Under such conditions, the astigmatic difference between the S and P wavefronts is completely eliminated at and beyond the second surface of the prism. However, in some instances the rate at which the spherical wavefront of the laser beam converges is so great that the focal power of one or more of the holographic facets, working in conjunction with the focal power of the incident laser beam is so great that the beam focuses at a point in the scanning field short of or beyond its prespecified focal plane. In order to compensate for this excessive or insufficient focal power, the disc designer may perform an additional stage of parameter adjustment to increase or decrease the radius of curvature of the resulting spherical wavefront so that when the spherical wavefront of the laser beam passes through each holographic facet on the scanning disc, the radius of curvature of the spherical wavefront will cause the wavefront to converge at the prespecified focal plane of the scanning pattern.

As indicated at Block E in FIG. 21B, the first step of this optional adjustment stage involves varying d to adjust the radius of curvature of the S cylindrical wavefront not significantly affected by variations in the prism tilt angle, and thereby cause both cylindrical wavefronts to focus to a focal point which will ensure that the beam focuses onto the focal plane of concern within the scanning volume of the holographic scanner. As indicated at Block F in FIG. 21B, the second step of the optional adjustment procedure involves adjusting the prism tilt angle until the radius of curvature of the cylindrical wavefront sensitive to prism tilt θ_(Prism-tilt) (i.e. the S wavefront) is once again equal to the radius of curvature of the other cylindrical wavefront, thus producing a spherical wavefront at the second surface of the prism which is converging along its optical axis. Inasmuch as this readjustment step seeks to achieve a desired focal length (i.e. the imaging distance) and eliminate astigmatic difference along the spherical wavefront of the laser beam, it is not possible to guarantee a circularized beam. In short, it is only possible to control precisely either ellipticity or focal length of the laser beam while eliminating astigmatism, but not both, in the second optical system.

As indicated at Block A in FIG. 21C, the first step of the second generalized parameter adjustment technique involves realizing values for all parameters in the geometrical optics model the second optical system except for the distance d and the incidence angles θ_(Pi1) and θ_(Pi2), which are treated as variables in the process. As indicated at Block B in FIG. 21C, the second step involves selecting an initial value for parameters d and θ_(Pi1) and θ_(Pi2) θ_(prism-tilt) which can be accomplished by virtually any criteria. Then as indicated at Block C in FIG. 21C, the procedure involves setting the distance d so that the S cylindrical wavefront, which is not sensitive to variations in prism tilt angle, is focused to a desired focal length, which may or may not be necessary to compensate for the focal power of the holographic facets, in relation to the prespecified focal planes in the scanning volume. In essence, this step at Block C presents a parameter constraint which the second system must satisfy. As indicated at Block D in FIG. 21C, the prism tilt angle is then adjusted so that the radius of curvature of the S cylindrical wavefront, which is not sensitive to prism tilt angle adjustment, is made equal to the radius of curvature of the P cylindrical wavefront, which is sensitive to prism tilt angle adjustment at the second surface of the prism, resulting in a spherical wavefront thereat which is converging along the optical axis of the second optical system. Under such conditions, the astigmatic difference between the S and P wavefronts is completely eliminated at and beyond the second surface of the prism. As the beam diameter (or aspect ratio) at the second surface of the prism is substantially equal to the beam diameter (i.e. aspect ratio) at the scanning disc, there is no need to readjust this parameter using a parameter readjustment stage of the type provided in the first parameter adjustment procedure.

When the design of the first and second optical systems of the laser beam production module have been completed, the next step of the process is to couple these systems. This step is achieved using plane mirror 63 which receives the astigmatism-free beam from the second surface of the prism and directs it through the diffractive grating at the predesigned incidence angle, at which it diffracts and ultimately falls incident on the rotating scanning disc. In essence, the plane mirror simply changes the direction of the laser beam from the prism and couples it to the diffraction grating without modifying the beam cross-section or other properties of the laser beam. In the illustrative embodiment, the plane mirror functions to fold the laser beam so that the aspheric collimating lens, prism and grating can be arranged in a manner to realize necessary parameters, while maintaining the volume within which the laser beam production module is realized. While a plane mirror has been used to couple the first and second optical systems together, it is understood that in other embodiments of the present invention, these systems can be directly coupled by proximate positioning, without the interposition of an optical component therebetween.

It is appropriate at this juncture to describe a specific procedure for assembling the components of the laser beam production module of the first illustrative embodiment, and configuring the geometrical and optical parameters thereof in accordance with the principles of the present invention. This particular procedure is based on the second generalized parameter adjustment method described above using the optical bench shown in FIG. 21A. As indicated in Blocks A, B and C of FIG. 21C1, the few steps of the procedure involve assembling the above-described subassembly upon the pivot plate. Specifically, the VLD 53A (53B, 53C) is first press fitted into one end of the VLD block 76. Then the aspheric collimating lens 61 is mounted in one end of the lens barrel 77. Then the lens barrel is screw-mounted into the VLD block by turning the same 3-4 turns. This step caries out the initial setting of the parameter d. As indicated at Block D, the VLD/lens subassembly is then attached to the VLD yoke 75 by way of pins 78A and 78B pivotally supporting the VLD and lens subassembly with one degree of rotational movement relative to the VLD yoke. Thereafter, at Block E the VLD yoke 75 is rotatably mounted to pivot plate 72 by way of pivot axis 73C, as shown in FIG. 21A. At Block F of FIG. 21C1, the pivot plate and optical subassembly mounted thereon is placed within fixture plates 87 of the parameter adjustment bench.

Without the prism not yet mounted to the pivot plate, the next stage of the procedure is carried out in order that the laser beam produced from the VLD and aspheric lens assembly is directed along an axis which will intersect the prism when mounted on the pivot plate and ensure that its entire beam cross-section falls incident upon the first surface of the prism. This stage of the procedure is carried out using the beam photodetector 91 mounted along axis 92, shown in FIG. 21A. The first step of this stage indicated at Block H involves tilting the VLD/lens subassembly within the yoke so that the laser beam is directed along target axis 92 and falls upon the quadrant-type photodetector. If necessary, one may adjust the beam size on the target by rotating the lens housing barrel 77 within the VLD block 76, and thus adjust the VLD-to-lens separation D. At Block I of FIG. 21C2, the yoke assembly is then rotated until the laser beam passes through the cross-hair of the target at the beam photodetector 91. So configured, the VLD and lens subassembly and yoke assembly are both locked in the position which ensures that the laser beam crosses through the target cross-hair, and thus the first surface of the prism.

The next stage of the procedure indicated at Block J of FIG. 21C2 involves installing the prism support plate 73 (with the prism premounted thereon) within the second mounting recess within the pivot plate, so that an initial value of prism tilt angle, θ_(prism tilt) is set. Then at Block K of FIG. 21C2, the lens barrel is adjusted relative to the VLD block, setting d so that the cross-sectional dimension of the beam in the non-scanning direction (i.e. parallel to code elements—bars and spaces) focuses to the focal length of the test lens 90 in FIG. 21A.

At this stage, an optical subassembly is provided having all of the essential components for configuring θ_(prism tilt) sufficient to eliminate astigmatism while achieving a desired beam aspect ratio.

Then Block L of FIG. 21C2 involves adjusting the prism tilt angle θ_(prism tilt) so that astigmatism is eliminated while achieving a particular beam aspect ratio. This stage involves the use of the Photon® Beam Scanning device to measure the beam cross-section of the laser beam in x and y directions, at different points along the optical axis of the prism, along which the beam propagates away from the second surface thereof. This prism tilt angle adjustment step is carried out selecting a prism tilt angle, and then measuring the beam cross-section along the beam. When the cross-sectional measures of the beam indicate that the beam converges to its focal point at the same rate along the x and y directions, and then diverges at equal rates in these orthogonal directions as one moves the point of measurement along the length of the beam, then the value of prism tilt angle, denoted θ^(*) _(prism-tilt), at which such conditions are detected is the prism tilt angle at which astigmatism is completely eliminated along the laser beam. Once obtained, this parameter θ^(*) _(prism-tilt) is locked into position using an adjustment screw and/or adhesive, as indicated at Block M of FIG. 21C2.

When the laser beam production module has been completely assembled and its parameters configured to eliminate astigmatism, the pivot plate is then mounted within the recess of the optical bench of the laser beam production module and then the pivot plate is rotated relative to module bench until the beam is perpendicular to the mirror, as indicated at Block N of FIG. 21C2. This step involves using the quadrant detector set-up along a different test optical axis. Then at Block O of FIG. 21C3, the light diffractive grating and mirror can be mounted within the support of the optical bench. Then at Block P of FIG. 21C3, the entire laser beam production module can be mounted on the optical bench of the scanning system, using alignment pins and holes, as illustrated in FIG. 21D. At this stage, the laser beam emanating from the second surface of the prism is automatically oriented along an axis which ultimately passes through the scanner disc in the plane formed between the (i) line extending from the outer scanning disc to Beam-Incident-Point point r_(o) and (ii) the scanning disc axis of rotation itself. At this stage of the construction process, angle of incidence θ_(i2) is automatically set so that the laser beam dispersion is minimized as the laser beam is diffracted through the scanning disc. This is achieved by physical construction of the scanner bench and module bench supporting the grating. Notably, angle of incidence θ_(i2) has been previously determined by the design process for the first optical system. Once the outgoing laser beam from the laser beam production module is aligned with respect to the scanning disc, the optical bench of the module can be fixed in place using bolts, screws or other fasteners known in the art. The above procedure is repeated for each of the other two laser beam production modules.

LASER BEAM PRODUCTION MODULE OF THE SECOND ILLUSTRATIVE EMBODIMENT

In FIG. 22, an alternative embodiment of the laser beam production module of the present invention is shown. In this second embodiment of the module, the use of a prism is eliminated. Instead, only a VLD 53A, an aspheric colliminating lens 61, a planar mirror 63 and a dual-function light diffraction grating 95 of fixed spatial-frequency are used to construct the module, as shown in FIG. 23. As shown in FIG. 23, all other components of the scanning system are the same.

In FIG. 23A, the components of the laser beam production module 12A′ (12B′, 12C′) of the second illustrative embodiment are shown assembled on the optical bench of the module, removed from the scanner housing. The construction of this embodiment of the laser beam production module is similar in many respects to the first illustrative embodiment, in that it has a pivot plate 72′ upon which a VLD yoke 75 is pivotally mounted for pivotally supporting VLD yolk Block 75. The VLD 53A and aspheric lens 65 are mounted with the lens barrel 77 as described above and this subassembly in turn is pivotally mounted within the VLD yoke 75. In this embodiment, there is a planar mirror 63 stationarily mounted with respect to module bench 60 by support elements. Also, the dual-function light diffraction grating 64′ is stationarily mounted with respect to the planar mirror. In order to adjust the angle of incidence at which the laser beam reflected off the planar mirror strikes the dual-function light diffraction grating, pivot plate 72′ is pivotally adjustable with respect to the optical bench of the laser beam production module in a manner to that provided in the first illustrative embodiment. Using this optical assembly, the laser beam production module can be realized, achieving the above-described objects of the invention.

As shown in FIG. 24, the method for designing the laser beam production module of the second illustrative embodiment of the present invention involves three basic steps. As indicated at Block A in FIG. 24, the first step involves designing a first optical system which includes the dual-function light diffractive grating 64′ and the holographic facets on the predesigned scanning disc. The first optical system has two principal functions, namely: to control the aspect-ratio of the incident laser beam on the scanning disc; and to minimize laser beam dispersion over the bandwidth of the VLD as the laser beam is diffracted through the rotating scanning disc. As indicated at Block B of FIG. 24, the second step of the design process involves designing a second optical system using the previously designed dual-function light diffractive grating. The principal function of the second optical system is to eliminate astigmatism along the laser beam at the second optical surface of the diffractive grating. At Block C of FIG. 24, the design process involves coupling the first and second optical systems using the planar mirror 63 to form a single unitary module which, when coupled with the scanning disc, performs the three above-described optical functions in a highly reliable manner. Each of these steps will be described in greater detail hereinafter.

Referring to FIGS. 25A through 25E and FIG. 26, the design of the first optical system of the laser beam production module of FIG. 23 will be described in detail.

As shown in FIG. 25A, a geometrical optics model is constructed for the first optical system, based on two assumptions, namely: (1) that the radius of curvature of the spherical wavefront incident the facet is very large relative to the surface area of the facet; and (2) that all light rays thereof are substantially collimated (i.e. the incident wavefront is substantially planar over the facet surface area). As shown in FIG. 25A and defined in the parameter description table of FIG. 25B, this model includes a number of external angles and distances, namely: D₁, the diameter of the laser beam leaving the aspheric collimating lens; D₂, the expanded diameter of the laser beam after emerging from the second surface of the dual-function diffractive grating; M, the beam diameter expansion ratio, defined as D₂/D₁; d₂, the average grating spacing of the facets on the scanning disc (in microns); θ_(i2), the incidence angle defined relative to a normal vector drawn to the first surface of an exemplary holographic facet on the scanning disc; diffraction angle θ_(d2), defined relative to a normal vector drawn to the second surface of the holographic facet; incidence angle θ_(i1), defined relative to a normal vector drawn to the first surface of the dual-function light diffraction grating; diffraction angle θ_(d1) defined relative to a normal vector drawn to the second surface of the light diffraction grating; θ_(i1M), the angle of incidence of the beam at the dual-function light diffraction grating that will provide the desired beam expansion ration, M; θ_(i1D), the angle of incidence of the beam at the dual-function light diffraction grating that will provide zero dispersion for the beam leaving the scanning disk; θ_(d1M), the angle of diffraction of the beam leaving the dual-function light diffraction grating that will provide the desired beam expansion ratio, M; θ_(d1D), the angle of diffraction of the beam leaving the dual-function light diffraction grating that will provide zero dispersion for the beam leaving the holographic disc; the orientation (i.e. tilt) angle ρ defined between the holographic disc and the multi-function light diffraction grating; and λ, the wavelength of the laser beam (in microns) produced from the VLD.

In FIG. 25C, a set of mathematical expressions are provided which define relationships between the parameters of the geometrical optics model. Expression No. 1 in FIG. 25C, derived from the well known grating equation, relates d₂, the “average grating spacing” of the fringe structures in the scanning disc, to the reconstruction wavelength of the VLD λ, and incidence angle θ_(i2) and diffraction angle θ_(d2). Using trigonometric relations, the angle of diffraction θ_(d1M) at which the desired beam expansion ratio occurs can be defined in terms of the tilt angle ρ and incidence angle θ_(i2) as defined by Expression No. 3 in FIG. 25C. Starting with the well known beam expansion ratio equation M=Cos(θ_(d1))/Cos(θ_(i1)), and applying some algebraic manipulation and Equation No. 3, a mathematical expression for the incidence angle θ_(i1M) can be derived in terms of tilt angle ρ, which will have the form of Expression No. 2 in FIG. 25C. Then using the grating equation, the grating spacing for the dual-function light diffraction grating can be derived as a function of the tilt angle ρ and the incidence and diffraction angles θ_(i1M) and θ_(d1M), respectively. This mathematical expression is set forth as Expression No. 4 in FIG. 25C.

Then using trigonometric relations, the angle of diffraction θ_(d1D) at which zero beam dispersion occurs is defined in terms of the tilt angle ρ and incidence angle θ_(i2) as defined by Expression No. 6 in FIG. 25C. Starting then with a zero dispersion equation similar to Expression No. 3 in FIG. 18C, and applying Expression No. 6 and some algebraic manipulation, an expression for the incidence angle θ_(i1D) is derived in terms of tilt angle ρ, incidence angle θ_(i2), reconstruction wavelength λ_(R) of the VLD, and d₂ (the average grating spacing of a fixed-spatial frequency equivalent of the holographic facets). This form of this expression is described by Expression No. 5 in FIG. 25C. Then using the grating equation once again, the grating spacing d_(1M)(ρ) associated with the dual-function light diffractive grating, is derived as a function of the tilt angle ρ, the incidence angle θ_(i1D) and wavelength λ_(R).

Thereafter, assuming values for parameters λ_(R), θ_(i2), M and θ_(d2), as set forth in the table of FIG. 25B1, Expressions 3 and 5 in FIG. 25C can be expressed solely as a function of tilt angle ρ. Notably, diffraction angle θ_(d2) is selected to be the average of the various diffraction angles (e.g. 37 degrees) associated with the sixteen holographic facets on the designed scanning disc of the illustrative embodiment. The beam expansion factor M, on the other hand, will typically be selected as the ratio of the two beam spread angles for the VLD used in the laser beam production module (e.g. M=3.0). However, in order to ease the manufacturing of the dual-function grating, the beam expansion factor M may be chosen somewhat smaller than the ratio of these beam spread angles. In the illustrative embodiment, the wavelength of the laser is 0.670 microns, whereas the angle of incidence at the scanning disk is 43 degrees while the corresponding angle of diffraction is 37 degrees, the average value thereof falling near the middle of the range of diffraction values for the 16 holographic facets on the scanning disk.

In order to find the value of tilt angle ρ at which both the conditions expressed in Expressions 2 and 5 are simultaneously satisfied, one of two solving techniques may be used. The first technique involves equating Expressions 2 and 5 in FIG. 25C equal to each other and then solving for tilt angle ρ. Alternatively, the second technique involves plotting the functions expressed in Expressions 2 and 5, as a function of tilt angle ρ, and identifying the value of tilt angle ρ₀ at which these functions intersect. Notably, by setting the tilt angle ρ between the scanning disk and the dual-function diffraction grating equal to ρ₀, the first optical system will achieve a beam expansion ratio of M=3.0 while minimizing beam dispersion over the bandwidth of the VLD producing the incident beam. In the illustrative embodiment, the value of tilt angle ρ₀ is equal to −11.1 degrees, at which the angle of incidence yielding the desired beam expansion ratio also equals the angle of incidence that yields minimum beam dispersion over the bandwidth of the incident laser beam produced by the VLD.

In FIG. 25E, a set of construction parameters are provided for the dual-function grating of the illustrative embodiment. Notably, these parameters are expressed at the reconstruction wavelength 670 nanometers, and thus must be converted to the construction wavelength of the Argon laser when the specified light diffraction grating is to be realized in DCG. The parameter conversion system and procedure of FIGS. 28A1 through 28D described above can be used for this purpose.

A post design tool available within the HSD workstation hereof, referred to as the “Beam Dispersion Analyzer” tool, is illustrated in FIGS. 27A through 27D1. This analytical tool can be used to analyze the variations of diffraction angle θ_(d2) for the laser beam leaving a designed scanning disc, geometrical modelled in FIG. 26. This tool is of great value in measuring the degree to which beam dispersion has been reduced when using a multi-function diffraction grating and any particular set of construction parameters (including parameters for tilt angle ρ) specified by the above-described design process.

As shown in FIG. 26, the second optical system designed above is geometrically modelled in a manner similar to that done during the design process. Parameters used to construct the geometric optics model are described in FIG. 27A. Given (assumed) parameters are set forth in FIG. 27B for the illustrative embodiment. Mathematical expressions describing important relations among certain of the parameters are set forth in FIG. 27C. In Expression No. 4 in FIG. 27C, the angle of diffraction θ_(d2) is expressed as a function of wavelength (in air) λ, tilt angle ρ, grating spacing d₁, grating spacing d₂, and incidence angle θ_(i1). Assuming parameter values for ρ, d₁, d₂, and θ_(i1), Expression No. 4 can be reduced to a function dependent solely on wavelength. Then by evaluating this resulting function using different values of wavelength within the bandwidth of the VLD, a plot of diffraction angle θ_(d2) can be plotted, as shown in FIGS. 27D and 27D1, a measure of beam dispersion derived. Notably, the laser bandwidth or spread from commercially available VLDs will be about 0.010 microns or less, and thus this will be a sufficient domain for λ. Typically, wavelength variations due to mode hopping are on the order of 0.0003 microns. With such assumed wavelength shifts from the VLDs in the scanning system, the resulting plot from the Beam Dispersion Analyzer indicates that first optical system of the module designed above will maintain the angular deviation (i.e. beam dispersion) of its diffracted laser beam to about 0.0055 degrees.

After completing the design of the first optical system of the laser beam production module, the dual-function light diffraction grating used therein can be constructed using holographic recording techniques. Using the grating equation, this fixed spatial-frequency light diffractive grating (HOE) can be uniquely specified by its reconstruction wavelength λ_(R) and the angle of incidence θ_(i1) and angle of diffraction θ_(i1) required by the design. However, as explained in connection with the design of the scanning disc and the laser beam production module of the first illustrative embodiment, it is easier to construct (i.e. fabricate) the dual-function diffraction grating at a construction wavelength λ_(C) different than reconstruction wavelength λ_(R), selected on the basis of the recording emulsion (e.g. DCG) used to realize the dual-function grating. The parameter conversion process illustrated in FIGS. 28A1 through 28D can be used to convert construction parameters for the dual-function grating, into a corresponding set of construction parameters expressed at the construction wavelength λ_(C). When calculating the exposure angles at the construction wavelength, the Bragg plane angle within the emulsion must be maintained constant after the construction process. As this process has been described in connection with the construction of each holographic facet on the scanning disc of the present invention, the details thereof will not be repeated herein to avoid redundancy. After the parameter conversion process of FIGS. 28A1 through 28D is carried out, the dual-function diffraction grating can be fabricated using the wavelength-converted parameters and the recording system illustrated in FIG. 29.

The next step in the design process entails designing the second optical system for the laser beam production module. In FIG. 30A, a geometrical optics model of the second optical system is shown. In the second illustrative embodiment, the sole function of this optical system is to eliminate astigmatism from the system. Consequently, the constraints imposed on this system design will differ from those applied in the first illustrative embodiment. As illustrated, the geometrical optics model comprises the VLD, the aspheric collimating lens, and the dual-function diffraction grating designed above as a fixed spatial-frequency holographic diffraction grating. Various geometrical and optical parameters of the geometrical optics model are indicated in FIGS. 30A, 30A1 and 30A2 and defined in detail in the table of parameters set forth in FIG. 30B. As described in FIG. 30B, the geometrical optics model of the second optical system is formed by the following parameters: f₁, the focal length of the aspheric collimating lens; S-source, the location of the source of the S cylindrical wavefront (i.e. S-beam source); P-source, the location of the source of the P cylindrical wavefront (i.e. P-beam source); d, the distance measured from the focal point of the collimating lens to the location of the source of the S cylindrical wavefront (i.e. S-beam source); δ, the distance between the S-source and the P-source (i.e. the astigmatic difference); D₁, the diameter of the P wavefront leaving the aspheric collimating lens; D₂, the diameter of the expanded P wavefront leaving the dual-function light diffraction grating; M, the beam expansion factor, defined as M=D₂/D₁; d_(h), the grating spacing of the dual-function light diffraction grating, measured in microns; θ_(Pi1), the angle of incidence of the lower portion of the converging P wavefront at the front surface of the dual-function light diffractive grating; θ_(Pi2), the angle of incidence of the upper portion of the converging P wavefront at the front surface of the dual-function light diffractive grating; φ_(P1), the angle of convergence of the P wavefront leaving the second surface of the aspheric collimating lens; φ_(S1), the angle of convergence of the S wavefront leaving the second surface of the aspheric collimating lens; φ_(P2), the angle of convergence of the P wavefront leaving the second surface of the dual-function light diffractive grating; φ_(S2), the angle of convergence of the S wavefront leaving the second surface of the dual-function light diffractive grating, which is equal to φ_(S1); L_(P1), the image distance for the P wavefront imaged by the aspheric collimating lens; L_(P2), the image distance for the P wavefront imaged by the aspheric collimating lens after insertion of the dual-function light diffractive grating; L_(S1), the image distance for the S wavefront imaged by the aspheric collimating lens; L_(S2), the image distance for the S wavefront imaged by the aspheric collimating lens, after inserting the dual-function light diffractive grating, which is equal to L_(S1); θ_(Pd1), the angle of diffraction of the lower portion of the converging P wavefront at the dual-function light diffractive element; θ_(Pd2), the angle of diffraction of the upper portion of the converging P wavefront at the dual-function light diffractive element; and λ_(R), the reconstruction wavelength of the laser beam produced from the VLD. Collectively, these parameters constitute the geometrical optics model of the second optical system of the second illustrative embodiment of the laser beam production module. Notably, the distance between the first surface of the dual-function holographic light diffractive grating and the principal plane of the collimating lens need not be considered as a parameter to the model provided that the entire cross-sectional diameter of the beam is incident (i.e. falls) upon the first surface of the light diffractive grating, which is a very easy assumption to satisfy in practice.

In FIG. 30B1, a set of assumed values are presented for various parameters in the model which can remain fixed during the design process, providing various coefficients in the mathematical expressions within the geometrical optics model. In FIGS. 30C1 and 30C2, a set of mathematical expressions are provided which define particular relationships between certain parameters in the geometrical optics model of the second optical system. As clearly illustrated, Expressions No. 1 to 12 lead to the derivation of equations for L_(P2) and L_(S2), given by Expressions Nos. 11 and 12 in FIGS. 30C1 and 30C2, the image distances of the P source and the S source after being imaged through the aspheric collimating lens and the light diffractive grating. From these functions, the curvature of the S cylindrical wavefront as it immediately emerges from the second surface of the light diffractive grating can be defined as 1/L_(S2), whereas the curvature of the P cylindrical wavefront as it immediately emerges from the second surface of the light diffractive grating can be defined as 1/L_(P2). Expressed in other words, the radius of curvature of the S cylindrical wavefront as it immediately leaves the second surface of the light diffractive grating is given by L_(S2), whereas the radius of curvature of the P cylindrical wavefront as it immediately leaves the second surface of the light diffractive grating is given by L_(P2). Mathcad 3.1 mathematical design program can be used to carry out geometrical optics modelling within the HSD Workstation of the present invention.

It is well known that each VLD having a non-zero astigmatic difference, defined herein as δ, will produce a laser beam which exhibits astigmatic properties. However, it has been discovered that, for each non-zero value of δ and assumed value of grating tilt angle θ_(grating-tilt) (i.e. grating incidence angles θ_(Pi1) and θ_(Pi2)), there exists a realizable value of d, at which the S and P cylindrical wavefronts leaving the second surface of the light diffractive grating have equal radii of curvature, as indicated in the plot shown in FIG. 30D. Under such optical conditions, both the S and P cylindrical wavefronts emerging from the second surface of the light diffractive grating are converging along the outgoing optical axis of the light diffractive grating at the same rate (by virtue of their equal radii of curvature) and the resulting wavefront is spherical and free of astigmatic aberrations associated with the non-zero inherent astigmatic difference in the VLD. The mathematical structure of the geometrical model for the second optical system suggests that, during the parameter adjustment procedure hereof, the geometrical parameter d functions as a variable or “adjustable parameter” while the grating tilt angle θ_(grating-tilt) parameter and θ_(Pi2) determined hereinabove function as constraints so that the optical conditions for astigmatism-elimination can be found during the adjustment procedure.

The optical functions performed by each of the components in the second optical system of this embodiment are similar to the functions performed by the components in the second optical system of the first illustrative embodiment. In particular, the S and P sources represented within the VLD produce cylindrical wavefronts emanating from the S and P source locations, respectively. The optical function of the aspheric collimating lens is to pass the S and P wavefronts, while changing the radii of curvature for both of these wavefronts as well as their apparent centers of curvature. In this embodiment of the second optical system, both the S and P wavefronts are assumed to propagate on axis, and therefore off-axis aberrations will be negligible and thus need not be considered. The optical function of the light diffractive grating in the second optical system is to significantly change the radius of curvature of only one of these cylindrical wavefronts, while minimally changing the radius of curvature of the other cylindrical wavefront. This significant degree of change in the radius of curvature is a strong function of the angles of incidence θ_(Pi1) and θ_(Pi2) measured with respect to the first surface of the light diffractive grating. This functional relationship and the manner in which such dependency is established among the various parameters in the analytical model of this optical system can be readily seen by carefully examining Expressions 1 through 12 set forth in FIGS. 30C1 and 30C2.

Importantly, the above analysis reveals that the design method of the second illustrative embodiment provides the designer with two degrees of freedom when finding the set of parameters that satisfies the optical condition illustrated in the plot shown in FIG. 30D. In particular, the designer may select a given value for the grating incidence angles θ_(Pi1) and θ_(Pi2), and then find the parameter value for parameters d which eliminates astigmatism at the second surface of the light diffractive grating. Alternatively, the designer may select a given value for the distance d, and then find the parameter value for grating tilt angle θ_(grating-tilt) which eliminates astigmatism at the second surface of the light. Notably, in this illustrative embodiment, the amount of tilt angle adjustment is quite small (e.g. 2-3 degrees maximum) due to the inherent Bragg angle sensitivity of the dual-function light diffractive grating of the laser beam production module.

Notably, the mathematical structure of the second optical system described above allows either (i) for the distance d to function as a system constraint in the parameter adjustment procedure, while the grating tilt angle θ_(grating-tilt) functions as the variable parameter therein, or (ii) for the grating tilt angle θ_(grating-tilt) to function as a system constraint in the parameter adjustment procedure, while the distance d functions as the variable parameter therein. Based on these two facts, two different parameter adjustment procedures have been developed to find the distance d or grating tilt angle θ_(grating-tilt) which eliminates astigmatism. While these techniques are based on the mathematical structure of the model used to find the conditions at which astigmatism is eliminated, they are not limited to laser scanning systems. In any particular design application, the procedure that will be used to configure the parameters of the optical system comprising a VLD, an aspheric collimating lens and a light diffractive grating, will depend on the physical constraints presented by the application at hand. For example, in designing the laser beam production module of the second illustrative embodiment where the grating tilt angle is predetermined when designing the first optical system thereof, the grating tilt angle θ_(grating-tilt) functions as a constraint during the design of the second optical system, whereas the distance parameter d functions as the variable parameter. In the case where a laser beam production module is being designed for a non-holographic laser scanner, and thus grating tilt angle θ_(grating-tilt) is not constrained to any particular value, then this parameter may function as a variable in the geometrical optics model of the optical system.

As mentioned in connection with the design of the laser beam production module of the first illustrative embodiment, it simply is not feasible in practice to empirically measure the astigmatic difference δ for each VLD to be used in the construction of a laser beam production module of the second illustrative embodiment. Consequently, it is not feasible to use the mathematical expressions set forth in the table of FIGS. 30C1 and 30C2 to compute the distance d for selected parameter values. Instead, the approach adopted by the design method of the second illustrative embodiment is to exploit the structure of the geometrical module described above and provide a novel procedure and bench for adjusting (i.e. configuring) the parameters of the second optical system to eliminate astigmatism. For clarity of exposition, the parameter adjustment bench will be described first, and thereafter, a generalized version of the parameter adjustment procedure with reference to the process diagram of FIG. 31B. Finally, a particular illustrative embodiment of the procedure will be described with reference to the parameter adjustment bench of FIG. 31A and process diagram of FIG. 31C.

In FIG. 31A, a parameter adjustment system 100 of the present invention is shown for use with the above-described laser beam production module. The function of this bench is to allow the parameters grating tilt angle θ_(grating-tilt) and distance d to be adjusted during the assembly/alignment procedure so that an astigmatism-free laser beam with a desired aspect-ratio is produced. As illustrated in FIGS. 31A1 and 31A2, the parameter adjustment system comprises an optical bench 101 upon which a pivot plate mounting fixture 102 is stationarily mounted. The function of the pivot plate mounting fixture is to mount during the parameter alignment procedure, an optical subassembly comprising module bench 60′ and pivot plate 72′ with the VLD, barrel, lens mount, and VLD yoke assembled thereon. The pivot plate mounting fixture provides a pivot plate mounting recess designed to securely receive the module bench 60′ and its associated optical subassembly.

As shown in FIGS. 31A1 and 31A2, the parameter adjustment system comprises beam scanning device 88 mounted on the optical bench along a first optical axis which, when the light diffractive grating 72′ is mounted on grating platform 70, passes through the center of the second surface of the light diffractive grating 72′ along an optical axis 103 passing through a scanning disc emulation hologram (H2) 104, a test lens (having length f_(test)) 105, and x-y beam scanner 88, as shown in FIG. 31A2. This adjustment mechanism allows the laser beam to be prealigned relative to the second surface of the light diffractive grating, without the light diffractive grating being mounted during the alignment step. The reason that scanning-disc emulation hologram 104 is required is because the dual-function diffraction grating, by itself, introduces dispersion which would affect the measurements without the use of a fixed frequency grating 104 which corresponds to an “average” holographic facet, with no focal power (e.g. θ_(i)=−43°, θ_(d)=37°). Notably, hologram 104 is tilted at angle ρ with respect to the dual-function grating to give zero beam dispersion. If the incidence angle θ (i.e. θ_(grating-tilt)) is changed during the design of the first optical system, then ρ preferably should be changed in order to improve the reduction of beam dispersion.

As shown in FIGS. 31A1 and 31A2, the parameter alignment bench also comprises a beam detector (e.g. quadrant-type photodetector) 91. The beam detector 91 is mounted on the optical bench along a second optical axis 106 which, when the light diffractive grating is mounted on grating platform 70 of module bench 60′, passes through the center of the first surface of the light diffractive grating 72′. As will be described below, these test instruments are used to adjust the geometrical and optical parameters of the laser beam production module during the assembly and configuration of the laser beam production module.

Generalized parameter adjustment technique, analogous to the generalized method described in FIG. 21B, will now be described with reference to FIG. 31B. Notably, this generalized technique is preferred inasmuch as it permits the dual-function grating to be fixedly mounted to the module bench, and thus predesigning the module bench and scanner bench so that automatic configuration of ρ is set upon mounting the module bench to the scanner bench via alignment pins 67 and 68. As indicated at Block A thereof, the first step of the technique involves realizing values for all parameters in the geometrical optics model of the second optical system except for (i) the distance d which is treated as a variable in the process and (ii) the grating angle θ_(grating-tilt) which is treated as a constraint in the design process. As indicated at Block B of FIG. 31B, the second step involves setting parameter θ_(grating-tilt) which is obtained from the design process of the first optical system of the laser beam production module of the second illustrative embodiment. Upon setting this parameter, the specified aspect ratio should be obtained. If the specified aspect ratio is not obtained upon setting parameter θ_(grating-tilt) to the value determined in the design process of the first optical system, the grating tilt angle should be adjusted until the desired aspect ratio is obtained. Then as indicated at Block C of FIG. 31B, the distance d is adjusted so that the radius of curvature of both the S and P cylindrical wavefronts are made equal at the second surface of the light diffractive grating, resulting in a spherical wavefront thereat which is converging along the optical axis of the second optical system. Under such conditions, the astigmatic difference between the S and P cylindrical wavefronts is completely eliminated at and beyond the second surface of the dual-function light diffractive grating.

Upon completing the design of the constituent optical systems of the laser beam production module of the second illustrative embodiment, the next step of the process, indicated at Block D of FIG. 31B, involves coupling together the first and second optical systems to provide a laser beam production module mounted on the scanner bench with precomputed incidence angle θ_(pi1) (i.e. θ_(grating-tilt)) and precomputed grating tilt angle ρset, minimizing laser beam dispersion over the bandwidth of the VLD. In this illustrative embodiment, the first and second optical systems of the laser beam production module are directly coupled without the use of an intermediate optical element, such as a planar mirror. However, in an alternative embodiment, a plane mirror may be used to fold the laser beam between the aspheric collimating lens and the light diffractive grating. This system coupling technique may be desirable in particular applications, where the aspheric collimating lens, and grating must be arranged in a manner relative to the scanning disc to realize a laser beam production module with miniature volumetric dimensions which must satisfy particular physical constraints.

It is appropriate at this juncture to describe a particular procedure for assembling the components of the laser beam production module of the second illustrative embodiment, and configuring the geometrical and optical parameters thereof in accordance with the principles of the present invention.

As indicated at Blocks A, B, C and D of FIG. 31C1, the first stage of the particular procedure involves assembling the above-described subassembly upon the pivot plate. Specifically, at Block A, the VLD is first press-fitted into one end of the VLD block 76. At Block B the aspheric collimating lens 61 is mounted in one end of the lens barrel 77. At Block C, the lens barrel is then screw mounted into the VLD block by turning the same 3-4 turns or so to set the distance parameter d to some initial value. At Block D, the VLD/lens subassembly is then attached to the VLD yoke 75 by way of pins 78A and 78B to pivotally support the VLD and lens subassembly with one degree of rotational movement relative to the VLD yoke. Thereafter, at Block E of FIG. 31C1, the VLD yoke is rotatably mounted to pivot plate 72′ shown in FIG. 23A. At Block F, the pivot plate and optical subassembly mounted thereon is then mounted on module bench 60′. At Block G, module bench 60′ with its subassembly shown in FIG. 23A, is then placed within the recess of the mounting fixture 102 of the parameter adjustment bench of FIGS. 31A1 and 31A2. At this stage of the assembly/adjustment procedure, indicated at Block H, electrical power is applied to the VLD so that it produces laser beam output.

The next stage of the procedure uses the beam photodetector 91 of the parameter adjustment system to align the produced laser beam with the first optical axis of the light diffraction grating. Without the dual-function light diffractive grating mounted to include bench 60′ and with the parameter adjustment bench arranged as shown in FIG. 31A1, the first step of this stage, indicated at Block I of FIG. 31C1, involves tilting the VLD/lens subassembly within the yoke so that the laser beam is directed along target axis 106 (i.e. to the first optical axis of the light diffractive grating) and falls upon the target (i.e. quadrant-type photodetector 91). At Block J at FIG. 31C2, the VLD yoke assembly is then rotated until the laser beam passes through the cross-hair of the target at the beam photodetector 91. Notably, the target position is selected so that when the grating and mirror are installed the laser beam strikes the mirror at a position which reflects the beam on Bragg through the dual function grating, as well as on an optical axis which is coplanar with the axis of rotation of the holographic scanning disc. When so configured, the VLD and lens subassembly and yoke assembly are both locked in the position.

The next stage of the procedure indicated at Block K of FIG. 31C2 involves installing the mirror 63 and dual function grating 72′ in module bench 60′ as shown in FIG. 31A2, using any suitable adhesive or equivalent means. With the diffraction grating and mirror mounted to the module bench, an optical subassembly is now provided having all of the essential components for configuring parameter d sufficient to eliminate astigmatism while achieving predetermined beam aspect-ratio.

As indicated at Block L of FIG. 31C2, the next stage of the procedure involves adjusting parameter d by rotating lens barrel relative to VLD block so that astigmatism is eliminated. This stage is carried out using the Photon® Beam Scanning device 88, volume hologram (H2) 103, and test lens 105 arranged in the manner illustrated in FIG. 31A2. While the VLD is actively driven and a laser beam emanating from the second surface of the light diffractive grating, parameter d is incrementally adjusted by rotating the lens barrel relative to the VLD Block C until astigmatism is eliminated. During this incremental adjustment process, the Photon® Beam Scanning device is used to measure the beam cross-section of the laser beam in x and y directions, at different points along the optical axis of the grating and colliminating lens along which the beam propagates. Specifically, this adjustment step is carried out by selecting a value for d, and then measuring the beam cross-section along the beam. When the cross-sectional measures of the beam indicate that the beam converges to its focal point at the same rate along the x and y directions, and then diverges at equal rates in these orthogonal directions as one moves the point of measurement along the length of the beam, then the value of distance d, denoted d^(*), at which such conditions are detected, is the value of d at which astigmatism is completely eliminated along the laser beam. When this parameter value for d is found by the above adjustment procedure, astigmatism is eliminated at the second surface of the light diffractive grating and therebeyond. This value of parameter d^(*) can then be locked with adhesive or other suitable means.

When the laser beam production module has been completely assembled and its parameters configured to eliminate astigmatism, then, as indicated at Block M in FIG. 31C2, the entire laser beam production module, preconfigured in the manner described above, is mounted on the optical bench of the scanning system as illustrated in FIG. 31D, so that alignment pins 68 on module bench 60′ fit into alignment holes 69 in scanner bench 5. At this stage of the assembly process, the grating tilt angle ρ₀ is automatically configured (i.e. set) so that laser beam dispersion is minimized as the laser beam is diffracted through the scanning disc. Notably, grating tilt angle ρ₀, previously determined by the design process for the first optical system, is set by the predesigned angle at which grating 72 is mounted on module bench 60′, relative to the geometry of scanner bench 5 and module bench 60′. Once the laser beam production module is aligned as described above, it is then fixed in place using bolts, screws or other fasteners known in the art. The above described procedure is repeated for each laser beam production module at each scanning station within the holographic laser scanner.

DESIGN OF THE LIGHT COLLECTING AND DETECTING SUBSYSTEM OF THE PRESENT INVENTION

Having described in great detail various procedures for designing and making holographic scanning discs and laser beam production modules according to the present invention, it is appropriate at this juncture to describe various light collection/detection subsystems for use in the holographic laser scanner of the present invention, and methods of designing the same.

As shown in FIGS. 14 and 22, the laser scanning system of the illustrative embodiment employs a light collecting/detecting subsystem which comprises three major subcomponents, namely: the holographic facet of the scanning disc 7 used to produce the P(i,j)th scanning plane from which reflected laser light being collected originated; a parabolic light focusing element (e.g. a parabolic focusing mirror) 14A (14B, 14C) mounted beneath the scanning disc adjacent each laser scanning station, and a photodetector 15A (15B, 15C) mounted above the scanning disc, along the focal axis of the parabolic light focusing mirror. As mentioned hereinabove, this subsystem design allows the scanner designer to minimize the height dimension of the scanner housing beneath the scanning disc, while the height of the beam folding mirrors determines the height of the scanner housing above the scanning disc.

The constraints which must be satisfied by an acceptable design for the light collection/detection subsystem of the present invention are specified as follows: (1) substantially all of the reflected light rays collected by any particular holographic facet during a light collection operation and focused by the parabolic light focusing mirror, pass through the particular holographic facet at an angle in which the light diffraction efficiency is minimal in order that maximal optical power is transmitted through the holographic facet towards the photodetector located at the focal point of the parabolic light focusing mirror; (2) the light rays reflected from a scanned code symbol falling incident on the inner and outer (i.e. extreme) portions of the holographic scanning disc during light collection operations (i.e. indicated as R₁ and R₂ in FIG. 34) are strongly diffracted by the scanning disc in a direction anti-parallel to the angle of incidence of the outgoing laser beam upon the scanning disc during laser beam scanning operations; and (3) the surface area of the parabolic focusing mirror is of such spatial extent and arranged relative to the scanning disc and photodetector that substantially all light rays collected by a particular holographic facet during a light scanning operation are received by the parabolic light focusing mirror as the holographic scanning disc rotates about its axis within the holographic laser scanner of the present invention. These constraints are important to the design and operation of the light collection subsystem shown in FIGS. 14 and 22, and as such, are embodied within the steps of the method for designing the light collection subsystem of the present invention described below. While possible, analytical expressions could be formulated for the geometrical optics model of the subsystem as shown in FIG. 32, and thereafter, optimal design parameters obtained through a rigorous mathematical analysis, as was employed with regard to the other subsystems of the holographic scanner hereof. However, the approach adopted below is to use the above-described subsystem constraints to provide a procedure for designing a suitable light collection subsystem for use with the previously designed scanning disc and laser beam production module of the present invention.

As indicated at Block A in FIG. 33A, the first step of the design method involves light diffraction efficiency analysis (i.e. Bragg sensitivity analysis) for each holographic facet in the previously designed scanning disc. The goal of this analysis is to determine, in the outgoing direction of the scanning disc, the angle of incidence relative to the Bragg angle of the facet (i.e. off Bragg), at which the light diffraction efficiency of the facets drops below a predetermined minimal threshold. Alternatively stated, the goal is to determine the angular range of incidence angles (e.g. from θ_(A) to θ_(B)) outside of which the diffraction efficiency of the holographic facet drops below the predetermined minimal threshold. This angular range is schematically illustrated in the geometrical model FIG. 34. As will be described below, this information is theoretically derived from an analysis of the diffraction efficiency of the facets with respect to particular polarization states of the light focused by the parabolic mirror. The mathematical expressions used to analyze such light diffraction efficiency as a function of incidence angle θ_(i) will differ for the different illustrative embodiments of the scanning disc hereof. In general, three types of holographic scanning disc may be used in any particular scanner design, namely: a scanning disc designed for use without cross-polarizers before the photodetectors; a scanning disc for use with P polarizers before the photodetectors; and a scanning disc for use with S polarizer before the scanning disc, as described above. Thus, Bragg sensitivity analysis for each of these three cases will be described below. In each case, a precise 3-D geometrical model of the holographic laser scanner under design is created, using the parameter values for the various subcomponents thereof determined in prior stages of the scanner design process hereof. Preferably, the 3-D geometrical model produced at this stage should not represent the parabolic light focusing mirrors 14A, 14B, 14C, nor the photodetectors 15A, 15B, 15C, as the precise geometry and relative position of the parabolic mirrors have not been specified at this stage of the design process, nor have the precise locations of the photodetectors been specified. The partial nature of the geometrical model is illustrated in FIG. 34. As will become apparent hereinafter, several critical design stages, involving light diffraction efficiency and ray tracing analysis, must first be performed before such specifications can be accurately obtained in accordance with the principles of the present invention.

As indicated at Block B of FIG. 33A, the next stage of the design process involves using the HSD workstation to perform a Bragg Sensitivity Analysis on each facet of the holographic scanning disc to determine the range of incident angles off Bragg, at which light rays reflected off the parabolic mirror will be transmitted through the facets with minimal diffraction towards the photodetector. The geometrical optics model shown in FIGS. 35A and 35B is used to represent the relevant geometrical and optical parameters used in the construction of a Bragg Light Diffraction Sensitivity Model of the holographic facets, based upon the original theoretical foundations laid down in Kogelnik's paper, supra. As the geometrical optics model of FIG. 35A1 is virtually identical to the model described in FIGS. 10A2 through 10B, it will not be necessary to repeat here the description of the geometrical and optical parameters comprising this model.

In FIGS. 35B1 and 35B2, a Bragg Light Diffraction Sensitivity Model is provided for the scanning disc designed for use without cross-polarizers before the photodetectors, shown in FIG. 10A1. This model contemplates that light of both S and P polarization states is reflected from a scanned code symbol, collected by the holographic facet, focused by the parabolic mirror and eventually transmitted through the holographic facet onto the photodetector for detection. Consequently, Expression No. 14 in FIG. 35C2 provides an expression for the “average” diffraction efficiency for light of S and P polarization states transmitted through each particular facet on the scanning disc, as a function of the angular deviation from the Bragg angle δ_(e). The constituent S and P diffraction efficiencies described by Expressions 12 and 13 of FIG. 35C2, respectively, are formulated using the assumed parameter values listed in the table of FIG. 35B1. The mathematical expressions set forth in Expressions No. 1 through 11 in FIG. 35C1 are derived by application of Snell's Law to the geometrical optics model of FIGS. 35A1 and 35A2, and principles of the Coupled Wave Theory in volume-type holographic light diffraction gratings, described in great detail in Herwig Kogelnik's paper, supra. Notably, while the “obliquity factors” C_(S) and C_(R) defined in Equations 6 and 7 are expressed in terms of the internal incidence angle α and the fringe slant angle φ, these parameters can be expressed in terms of θi and θd, as discussed in Kogelnik's paper.

The functions plotted in FIGS. 35D1 and 35D2 show the “normalized” average light diffraction efficiency for the first and sixteenth holographic facet, expressed as a function of the angular deviation from the Bragg angle, δ_(e). Expression No. 14 is used to produce such graphical plots. For δ_(e)=0, which is the case where the angle of incidence is equal to the Bragg angle of the holographic facet, the theoretical average light diffraction efficiency is maximum (i.e. E_(norm./avg.)=1) as one would expect. For angles of incidence away from the Bragg angle of the facet, the light diffraction efficiency generally decreases, with some oscillatory behavior. By evaluating and plotting the “normalized” average light diffraction efficiency for each holographic facet, the subsystem designer can identify, for each holographic facet, at which angle off Bragg δ_(e) the normalized light diffraction efficiency is below a minimal threshold (e.g. 0.09). Using such angular information, the designer can determine at which angles focused light rays from the parabolic mirror must be transmitted through the holographic facets with minimal diffraction, and thus maximum power transfer for detection. Notably, it has been found during such analysis that in order to reflect the collected light rays back through the scanning disk toward the photodetector without significant diffraction losses, the angle of incidence of each and every one of the light rays from the complete bundle of light rays from the parabolic mirror, must be at least 20 degrees away from the outgoing beam angle of incidence (i.e. the outgoing Bragg angle).

Referring to FIGS. 37A through 37C2, and the geometrical optics model of the scanning disc shown in FIGS. 28A1 and 28A2, a Bragg Light Diffraction Sensitivity Model will be described for analyzing the scanning disc designed with an S polarizer placed before the photodetectors, as shown in FIG. 36 i.e., when using the laser beam production module of the second illustrative embodiment. This model contemplates that light of P polarization state is used to scan a code symbol, and light of S polarization state is reflected from a scanned code symbol, collected by the holographic facet, focused by the parabolic mirror and eventually transmitted through the holographic facet onto the photodetector for detection. The S polarizer allows light rays of S polarization to pass onto the photodetector, whereas light rays of P polarization state are filtered out by the polarizer. Consequently, Expression No. 12 in FIG. 37B provides a general expression for the diffraction efficiency of each particular facet on the scanning disc to light of S polarization state transmitted therethrough. Notably, this characteristic of each facet is expressed as a function of the angular deviation from the Bragg angle δ_(e) and has been formulated using the assumed parameter values listed in the table of FIG. 37A1. The mathematical expressions set forth in Expressions No. 1 through 11 are derived by application of Snell's Law to the geometrical optics model of the volume-type holographic facets on the scanning disc, as shown in FIGS. 35B1 and 35B2. The “obliquity factors” C_(S) and C_(R) defined in Expressions No. 6 and 7 of FIG. 37B are derived using the well known principles of the Coupled Wave Theory in volume-type holographic gratings. The functions plotted in FIGS. 37C1 and 37C2 show the “normalized” light diffraction efficiency for the holographic facets No. 1 and 16 to S polarized light, expressed as a function of the angular deviation from the Bragg angle, δ_(e). Expression No. 12 in FIG. 37B is used, to produce such graphical plots. For δ_(e)=0, which is the case where the angle of incidence is equal to the Bragg angle of the holographic facet, the theoretical light diffraction efficiency of each facet to S polarized light is maximum (i.e. E_(norm.)=1) as one would expect. For angles of incidence away from the Bragg angle of the facet, the light diffraction efficiency generally decreases, with some oscillatory behavior. By evaluating and plotting the “normalized” light diffraction efficiency for each holographic facet, the subsystem designer can identify, for each holographic facet, at which angle off Bragg δ_(e) the normalized light diffraction efficiency is below a minimal threshold (e.g. 0.09). By analyzing such plots, the designer can then determine at which angles focused light rays from the parabolic mirror must be transmitted through the holographic facets with minimal diffraction, and thus maximum power transfer for detection.

Referring to FIGS. 38A through and the geometrical optics model of the scanning disc shown in FIGS. 28A1 and 28A2, a Bragg Light Diffraction Sensitivity Model is provided for the scanning disc designed for use with a P state polarizer placed before the photodetectors, as shown in FIG. 36 i.e., when using the laser beam production module of the first illustrative embodiment hereof. This model contemplates that light of S polarization state is used to scan a code symbol, and light of P polarization state is reflected from a scanned code symbol, collected by the holographic facet, focused by the parabolic mirror and eventually transmitted through the holographic facet onto the photodetector for detection. The P polarizer allows light rays of P polarization state to pass onto the photodetector, whereas light rays of S polarization state are filtered out by the polarizer. Consequently, Expression No. 12 in FIG. 38B2 provides a general expression for the diffraction efficiency of each particular facet on the scanning disc to light of P polarization state transmitted therethrough. Notably, this characteristic of each facet is expressed as a function of the angular deviation from the Bragg angle δ_(e) and has been formulated using the assumed parameter values listed in the table of FIG. 38A1. The mathematical expressions set forth in Expression Nos. 1 through 11 of FIG. 38B1 are derived by application of Snell's Law to the geometrical optics model of the volume-type holographic facets on the scanning disc, as shown in FIGS. 35A1 and 35A2. The “obliquity factors” C_(S) and C_(R) defined in Expressions 6 and 7 of FIG. 38B1 are derived using the well known principles of the Coupled Wave Theory in volume-type holographic gratings. The functions plotted in FIGS. 38C1 through 38C2 show the “normalized” light diffraction efficiency for holographic facet Nos. 1 and 16 to P polarized light, expressed as a function of the angular deviation from the Bragg angle, δ_(e). Expression No. 12 is used to produce such a family of graphical plots. For δ_(e)=0, which is the case where the angle of incidence is equal to the Bragg angle of the holographic facet, the theoretical light diffraction efficiency of each facet to P polarized light is maximum (i.e. E_(norm.)=1) as one would expect. For angles of incidence away from the Bragg angle of the facet, the light diffraction efficiency generally decreases, with some oscillatory behavior. By evaluating and plotting the “normalized” light diffraction efficiency for each holographic facet, the subsystem designer can identify, for each holographic facet, at which angle off Bragg δ_(e) the normalized light diffraction efficiency is below a minimal threshold (e.g. 0.09). By analyzing such plots, the designer can then determine at which angles focused light rays from the parabolic mirror must be transmitted through the holographic facets with minimal diffraction, and thus maximum power transfer for detection.

Having completed the Bragg Sensitivity Analysis required for the type of scanning disc employed in the scanner under design, the subsystem designer can then locate the position (e.g. center and optical axis orientation) of the photodetectors above the scanning disc. As indicated at Block C in FIG. 33A, this step involves using the HSD workstation to conduct an accurate ray training analysis of all incoming light rays reflected from a code symbol anywhere in the scanning volume onto the facets of the scanning disc, and based on this analysis, identifying a point above the scanning disc (but below the top edge of the beam folding mirrors) which is free of incoming light rays. At Block D, use the ray free points to locate the position of the photodetectors.

As indicated at Block E in FIG. 33A, the next step in the subsystem design method involves selecting a generalized parabolic surface function S_(parabolic)(x,y,z) for use in specifying the light collection/focusing mirror of each light collection subsystem. As will be described below, the balance of the subsystem design method then involves specifying the parameters of the parabolic surface patch, from which the parabolic mirror can be constructed.

As indicated at step F in FIG. 33B, the next step of the subsystem design process involves extending the geometrical optics model of the subsystem by adding to the geometrical optics model of FIG. 34, a line which extends from the center location of the photodetector, parallel to and preferably above the line of laser beam incidence to the scanning disc, as shown in FIG. 39. The function of this line is to establish the position and orientation of the optical axis of the yet, unspecified parabolic surface path representative of the parabolic mirror to be constructed and installed beneath the scanning disc, adjacent the laser beam production module.

As indicated at Block G of FIG. 33B, the next step of the design method involves specifying the focal length of the parabolic surface patch. The focal length of the parabolic surface patch will typically be determined primarily by the spatial restrictions beneath the scanning disc. In the holographic laser scanner of the illustrative embodiment, the focal length for the parabolic surface was chosen to be 3.0 inches as this is provided sufficient space below the scanning disc to mount the parabolic mirror. It is understood, however, this parameter will typically vary from embodiment to embodiment.

As indicated at Block H in FIG. 33B, the next step of the design method involves determining which holographic facet on the scanning disc has the smallest inner radius, r_(i). By its very geometry, this facet will collect light rays closest to the center (i.e. hub) of the scanning disc, and thus will diffract light rays closest to the axis of rotation thereof. Thereafter, use this facet to determine the lengthwise dimension of the parabolic surface patch, as shown in FIG. 39. Notably, for purposes of design, the extreme (i.e. inner and outer) light rays falling on this facet are assumed to strike the surface thereof at the Bragg angle of the facet, and thus by design, the diffracted light rays are transmitted towards the parabolic surface in a direction parallel to the optical axis of the parabolic surface path. In this way, when the parabolic mirror is realized according to the specification of the parabolic surface patch, collected light rays falling incident on a facet close to the Bragg Angle thereof will be focused to the focal point of the parabolic light focusing surface, at which the photodetector is located.

As indicated at Block I of FIG. 33C, the next step of the design method involves determining which holographic facet on the scanning disc has the greatest angular rotation, θ_(rot). As will be described below, this facet will be used to specify the widthwise dimension of the parabolic surface patch. The lower bound set on the widthwise dimension of the parabolic surface patch is the design constraint requiring that substantially all light rays collected by a particular holographic facet during a light scanning operation are received by the parabolic mirror as the holographic scanning disc rotates about its axis of rotation. The upper bound on the widthwise dimension of the parabolic surface patch is the available space beneath the scanning disc, within the spatially-constrained housing.

At Block J of FIG. 33C, the subsystem designer uses the 3-D geometrical optics model of the scanner developed heretofore on the HSD workstation and the facet with the greatest angular sweep to determine the minimal left and right surface boundaries that may be imposed upon the widthwise dimensions of the parabolic surface patch. Below is a technique for determining these surface boundaries.

As shown in FIG. 40A, the minimal left surface boundary is determined by computer modelling in 3-D, the situation where the incident laser beam has just begun to illiminate the rightmost edge of the above-identified holographic facet. Ideally, at this stage of the scanline generation process, all of the reflected light rays reflected off the beam folding mirror are collected by the holographic facet. However, to ensure that all such light rays collected by the facet at this stage of the scanning operation are collected ny the parabolic light focusing mirror for focusing, the designer extends outwardly the leftmost surface boundary of the parabolic surface patch just so that the entire facet is disposed beneath the parabolic surface patch.

Then as shown in FIG. 40B, the minimal right surface boundary is determined by computer modelling in 3-D, the situation where the incident laser beam is just about finished illuminating the leftmost edge of the above-identified holographic facet. Ideally, at this stage of the scanline generation process as well as at other instances thereof, all of the reflected light rays reflected off the beam folding mirror are collected by the holographic facet. To ensure that all such light rays collected by the facet at this stage of the scanning operation are collected by the parabolic light focusing mirror for focusing, the designer extends outwardly only the rightmost surface boundary of the parabolic surface patch just so that the entire facet is disposed beneath the parabolic surface patch.

Having completed the above steps, the widthwise surface dimensions can be determined by projecting the boundaries determined at the scanning disc plane, onto the 3-D parabolic surface patch. Collectively, the lengthwise and projected widthwise dimensions of the parabolic surface patch provide “patch cutting parameters” that can be used to construct a parabolic mirror for the light collection subsystem under design. A preferred way of constructing the parabolic mirror is to use the patch cutting parameters to cut out a parabolic patch from a parabolic mirror having the focal distance specified at block G of the design procedure. Notably, the resulting parabolic mirror designed above, will cover the entire area of the light collecting portion of the largest facet over the entire sweep width as the scanning disc rotates.

Then at Block K of FIG. 33C, the 3-D geometrical model of the light collection/detection subsystem is revised on the HSD workstation using the complete set of specifications for the parabolic surface patch (i.e. parabolic mirror). Then as indicated at Block L of FIG. 33C, the updated geometrical model is carefully analyzed on the HSD workstation to confirm that all light rays reflected off the parabolic mirror are transmitted through the respective holographic facets off Bragg, to ensure that maximum optical power is transmitted to the photodetector at the focal point of the parabolic mirror of the light detection subsystem. If this ray tracing analysis proves that the subsystem design satisfies the specified criteria, then the design process is completed and the subsystem design can then be realized according to the final geometrical model. If, however, the ray tracing analysis indicates the design falls short of satisfying its criteria, the designer can return to any one or more of the above-described steps in the procedure, modify the parameters thereat, and proceed through the design process until the desired performance criteria is satisfied. Typically, one run through this design procedure is all that will be required to achieve a satisfactory subsystem design which satisfies the system contraints presented at this stage of the overall scanner design process.

In FIG. 41, the holographic laser scanner hereof is shown with an alternative embodiment of the light detection subsystem of the present invention. Instead of using a parabolic mirror to focus collected light rays towards a photodetector located at the focal point of the parabolic mirror, this scanning system empolys a reflection-volume hologram 108 to perform such an optical funcation. In all other respects, the light detection subsystem of FIG. 41 is similar to the illustrative embodiment described in detail hereinabove. Notably, the design techniques described above can be used to design the reflection-volume hologram 108 of the light detection subsystem. 

What is claimed is:
 1. An automatic laser scanning bar code symbol reading system for automatically reading bar code symbols on packages transported through a 3-D scanning volume, said automatic laser scanning bar code symbol reading system comprising: a conveyor belt along which packages bearing bar code symbols are transported; a holographic-based bar code position detector, mounted above said conveyor belt, employing one or more laser beam sources and a holographic scanning disc for producing a first laser scanning pattern within said 3-D scanning volume, for scanning each said package transported along said conveyor belt, detecting the position of the bar code symbol on said package within said 3-D scanning volume, and automatically producing bar code position data specifying the position of the detected bar code symbol within said 3-D scanning volume; and a laser scanning bar code symbol reader, mounted above said conveyor belt, responsive to said bar code position data, and automatically steerable as so to laser scan said detected bar code symbol, and produce scan data indicative of said detected bar code symbol, and automatically process said produced scan data so as to automatically read said detected bar code symbol and produce symbol character data representative thereof.
 2. The automatic laser scanning bar code symbol reading system of claim 1, wherein said laser scanning bar code symbol reader comprises a laser scanning mechanism for automatically (i) producing a second laser scanning pattern within said 3-D scanning volume near which said bar code symbol is detected, (ii) laser scanning said detected bar code symbol using said second laser scanning pattern, and (iii) producing said scan data indicative of said scanned bar code symbol.
 3. The automatic laser scanning bar code symbol reading system of claim 1, wherein said first laser scanning pattern is an omnidirectional laser scanning pattern produced within said 3-D scanning volume, for detection of the bar code symbol on each package transported through said 3-D scanning volume.
 4. The automatic laser scanning bar code symbol reading system of claim 3, wherein said omnidirectional laser scanning pattern has at least four focal zones and a depth of field of at least 24 inches.
 5. The automatic laser scanning bar code symbol reading system of claim 2, wherein said second laser scanning pattern is an X-bar laser scanning pattern.
 6. The automatic laser scanning bar code symbol reading system of claim 1, wherein wherein said laser scanning bar code symbol reader comprises a bar code symbol decoder for automatically decode processing said produced scan data.
 7. The automatic bar code symbol reading system of claim 5, wherein said bar code symbol decoder employs bar code stitching processes during said decode processing.
 8. The automatic laser scanning bar code symbol reading system of claim 2, wherein said laser scanning mechanism further comprises a video buffer for collecting frames of produced scan data as said package is transported through said 3-D scanning volume and said detected bar code symbol is scanned by said second laser scanning pattern.
 9. The automatic laser scanning bar code symbol reading system of claim 6, wherein said bar code symbol decoder comprises a decode computer for decode processing each frames of produced scan data collected by said video buffer.
 10. A method of reading bar code symbols on packages transported through a 3-D scanning volume, said method comprising the steps of: (a) transporting packages bearing bar code symbols along a conveyor belt, over which a holographic-based bar code position detector and a laser scanning bar code symbol reader are mounted, said holographic-based bar code position detector employing one or more laser beam sources and a holographic scanning disc for producing said first laser scanning pattern within said 3-D scanning volume; (b) using said first laser scanning pattern to scan each said package transported along said conveyor belt; (c) detecting the position of the scanned bar code symbol using said holographic-based bar code position detector, and automatically producing bar code position data specifying the position of the detected bar code symbol within said 3-D scanning volume; (d) using the bar code position data produced during step (c) to automatically steer said laser scanning bar code symbol reader so as to automatically laser scan said detected bar code symbol, and produce scan data indicative of said detected bar code symbol; and (e) automatically processing said produced scan data so as to read said detected bar code symbol and produce symbol character data representative said detected bar code symbol.
 11. The method of claim 10, wherein during step (d) said laser scanning bar code symbol reader comprises a laser scanning mechanism for automatically (i) producing a second laser scanning pattern within said 3-D scanning volume near which said bar code symbol is detected, (ii) scanning said detected bar code symbol using said second laser scanning pattern, and (iii) producing said scan data.
 12. The method of claim 10, wherein during step (b) said first laser scanning pattern has at least four focal zones and a depth of field of at least 24 inches.
 13. The method of claim 10, wherein during step (b) said first laser scanning pattern is an omnidirectional laser scanning pattern produced within said 3-D scanning volume, for detection of the bar code symbol on each package transported through said 3-D scanning volume.
 14. The method of claim 11, wherein during step (d) said second laser scanning pattern is an X-bar laser scanning pattern.
 15. The method of claim 9, wherein step (e) comprises automatically decode processing said produced scan data so as to decode said detected bar code symbol within said 3-D scanning volume.
 16. The method of claim 15, wherein step (e) employs bar code stitching processes during said decode processing.
 17. The method of claim 11, wherein step (d) further comprises using a video buffer for collecting frames of scan data produced as said package is transported through said 3-D scanning volume and said detected bar code symbol is scanned by said second laser scanning pattern.
 18. The method of claim 17, wherein step (e) comprises using a decode computer for decode processing each frames of scan data collected by said video buffer. 